Development of High Performance Concrete and Evaluation of

Research Final Report

for

Research Project T2696, Task 02

Development Of High Performance Concrete And

Evaluation Of Construction Joints In

Concrete Floating Bridges

DEVELOPMENT OF HIGH PERFORMANCE CONCRETE AND

EVALUATION OF CONSTRUCTION JOINTS IN

CONCRETE FLOATING BRIDGES

by

Rafik Itani, Eyad Masad, Bart Balko and Brian Bayne

Washington State Transportation Center (TRAC)

Department of Civil and Environmental Engineering

Washington State University

Pullman, WA 99164

Washington State Department of Transportation

Technical Monitor

Geoff Swett, Bridge Engineer

Prepared for

Washington State Transportation Commission

Department of Transportation

and in cooperation with

US Department of Transportation

Federal Highway Administration

July, 2003

TECHNICAL REPORT DOCUMENTATION PAGE

1. Report No.

WA-RD 649.1

2. Government Accession No. 3. Recipient’s Catalog No.

4. Title and Subtitle

DEVELOPMENT OF HIGH PERFORMANCE CONCRETE AND EVALUATION

OF CONSTRUCTION JOINTS IN CONCRETE FLOATING BRIDGES

5. Report Date

July 2003

6. Performing Organization Code

7. Author(s)

Rafik Itani, Eyad Masad, Bart Balko, Brian Bayne

8. Performing Organization Report No.

9. Performing Organization Name and Address

Washington State Transportation Center (TRAC)

Civil and Environmental Engineering; Sloan Hall, Room 101

Washington State University

Pullman, Washington 99164-2910

10. Work Unit No.

11. Contract or Grant No.

T2696 Task 02

12. Sponsoring Agency Name and Address

Research Office

Washington State Department of Transportation

Transportation Building, MS 7370

Olympia, Washington 98504-7370

13. Type of Report and Period Covered

Final Report

14. Sponsoring Agency Code

15. Supplementary Notes

This study was conducted in cooperation with the U.S. Department of Transportation, Federal Highway Administration.

16. Abstract

Floating bridge concrete must be watertight, durable, workable, and must have sufficient cohesiveness to prevent segregation in

heavily congested deep walls. The mix design must experience minimal creep and shrinkage to reduce prestress losses, and

shrinkage cracking. As a result of recent concrete research, new mixes were created incorporating various quantities of fly ash,

silica fume, metakaolin, poly-carboxylate ether superplasticizers, and Caltite waterproofing admixture. This research focuses on

concrete with a water binder ratio of 0.33 and a slump in the range of 8 to 9 inches. Workability characteristics of the fresh

concrete are analyzed and hardened concrete properties tested in this research are compressive strength, chloride ion permeability,

and creep and drying shrinkage properties.

It was found that metakaolin was successful in producing mix designs with similar properties as Silica fume modified concrete.

Satisfactory strength was achieved through increasing the fly ash and lowering the silica fume contents, though, chloride ion

permeability was negatively affected. The removal of silica fume and the inclusion of Caltite decreased the concrete’s resistance to

chloride ion permeability and produced concrete that failed to attain the required 28-day ultimate compressive strength of 6500 psi.

The second part of this study focuses on developing an experimental setup to evaluate products and construction methods to help

prevent water leakage through construction joints in pontoon floating bridges. A pressure system was used to apply significant

pressures to concrete test specimens containing a construction joint. Different products and construction methods were used in

constructing the joints to determine the most effective methods for preventing water penetration in the field.

The testing results have shown compaction effort is the most important factor in water leakage through a joint. Increased

compaction in laboratory specimens leads to less water leakage through construction joints. Product selection was ineffective in

preventing water leakage if concrete compaction was inadequate.

17. Key Words

Concrete, Performance, Fly Ash, Silica Fume, Metakaolin,

Polycarboxylate, Caltite, Creep, Shrinkage, Compressive Strength,

Permeability, Construction Joint, Leakage, Waterstop, Compaction,

Watertight

18. Distribution Statement

No restrictions. This document is available through the

National Technical Information Service, Springfield, VA

22161.

19. Security Classif. (of this report)

None

20. Security Classif. (of this

page)

None

21. No. of Pages

239

22. Price

Form DOT F 1700.7 (8-72)

Reproduction of completed page authorized

DISCLAIMER

The contents of this report reflect the views of the authors, who are responsible for the facts and accuracy

of the data presented herein. The contents do not necessarily reflect the official views or policies of the

Washington State Transportation Commission, Department of Transportation, or the Federal Highway

Administration. The report does not constitute a standard, specification, or regulation.

iv

TABLE OF CONTENTS

LIST OF TABLES............................................................................................................ vii

LIST OF FIGURES ........................................................................................................... ix

SUMMARY ....................................................................................................................... 1

CHAPTER 1: INTRODUCTION .................................................................................. 2

1.1 Background......................................................................................................... 2

1.2 Problem Statement.............................................................................................. 3

1.3 Objectives ........................................................................................................... 6

1.4 Task Summary .................................................................................................... 7

CHAPTER 2: LITERATURE REVIEW ..................................................................... 10

2.1 Concrete for the Lacey V. Murrow Floating Bridge......................................... 10

2.2 Creep of Concrete ............................................................................................. 12

2.2.1 Creep affected by concrete composition................................................... 15

2.2.2 Creep related to compressive strength and shrinkage............................... 24

2.3 Other Concrete materials and Admixtures........................................................ 28

CHAPTER 3: EXPERIMENTAL METHODS............................................................ 32

3.1 MATERIALS and Mix Designs ....................................................................... 32

3.2 Creep................................................................................................................. 41

3.3 Shrinkage .......................................................................................................... 52

3.4 Compressive Strength ....................................................................................... 53

3.5 Chloride Ion Penetration................................................................................... 54

v

CHAPTER 4: EXPERIMENTAL RESULTS AND ANALYSIS ............................... 56

4.1 Concrete Mix Designs....................................................................................... 57

4.2 Creep................................................................................................................. 58

4.3 Shrinkage .......................................................................................................... 69

4.4 Compressive Strength ....................................................................................... 72

4.5 Chloride Ion Penetration................................................................................... 75

CHAPTER 5: Summary and Conclusions ................................................................... 80

REFERENCES................................................................................................................ 83

CHAPTER 6: LITERATURE REVIEW ..................................................................... 87

6.1 Floating Bridge History .................................................................................... 87

6.2 Hood Canal Design and Construction............................................................... 87

6.3 Mix Design........................................................................................................ 89

6.4 Water Leakage Tests through Cracked Concrete Elements.............................. 90

6.5 Moist Curing and Permeability......................................................................... 95

6.6 Waterstop Testing ............................................................................................. 96

6.7 Compaction Level for Concrete Construction Joints........................................ 97

6.8 Summary........................................................................................................... 98

CHAPTER 7: MATERIALS AND TESTING METHODS........................................ 99

7.1 Mix Design Specifications................................................................................ 99

7.2 Test Specimens ................................................................................................. 99

7.3 Products and Construction Methods Tested ................................................... 114

7.4 Experiment 1................................................................................................... 120

7.5 Experiment 2................................................................................................... 127

vi

7.6 Experiment 3: Waterstop Testing ................................................................... 137

CHAPTER 8: TEST RESULTS................................................................................. 139

8.1 Mix Characteristics ......................................................................................... 139

8.2 Experiment 1 Test Results .............................................................................. 139

8.3 Experiment 2 Test Results .............................................................................. 140

8.4 Third Experiment: Test Results ...................................................................... 153

CHAPTER 9: CONCLUSIONS AND RECOMMENDATIONS ............................. 159

9.1 Conclusions..................................................................................................... 159

9.2 General Guidelines for Watertight Joint ......................................................... 161

9.3 Recommendations for Further Study.............................................................. 161

REFERENCES ............................................................................................................... 164

APPENDIX A................................................................................................................ 166

APPENDIX B ................................................................................................................ 216

APPENDIX C................................................................................................................ 219

vii

LIST OF TABLES

Table 2.1 - Trends in Concrete Creep............................................................................... 20

Table 3.1 – Mix #1 LVM Mix Design, Reference Mix Design....................................... 36

Table 3.2 – Mix #2 1st Alteration - WJE, Inc. Report Recommendation........................ 36

Table 3.3 – Mix # 3 - 2nd Alteration - Metakaolin - 5% OPC Replacement ................... 37

Table 3.4 – Mix # 4 - 3rd Alteration - Metakaolin - 10% OPC Replacement .................. 37

Table 3.5 – Mix # 5 - LVM Mix Design #2 - Reference Mix Design .............................. 38

Table 3.6 – Mix # 6 - 4th Alteration - LVM Mix with Caltite Admixture ....................... 38

Table 3.7 – Mix # 7 - 5th Alteration - Caltite Mix Design ............................................... 39

Table 3.8 - Aggregate Gradations.................................................................................... 39

Table 3.9 - Total Aggregate Blend Gradation .................................................................. 40

Table 3.10 - Temperature and Humidity History.............................................................. 52

Table 4.1 - HPC Performance Grades (Table 1.2 - Definition of HPC according to

Federal Highway Administration, Goodspeed, et al. 1996)...................................... 56

Table 4.2 - Concrete Mix Design Quantities .................................................................... 57

Table 4.3 - Creep Comparison.......................................................................................... 60

Table 4.4 – Shrinkage Strains ........................................................................................... 71

Table 4.5 – 28-Day Compressive Strength....................................................................... 74

Table 4.6 – Rapid Chloride Permeability Test Results - 28 day...................................... 78

Table 4.7 – Permeability Classifications .......................................................................... 78

Table 5.1 – Mix Design Test Results................................................................................ 80

Table 7.1 LVM Mix Design (after Lwin et al. 1995). ...................................................... 89

Table 8.1 Mix Design ..................................................................................................... 104

viii

Table 8.2 Final Mix Design ............................................................................................ 105

Table 8.3 - Products tested in experiments. .................................................................... 115

Table 8.4 - Construction methods tested in experiments................................................ 115

Table 8.5 - Stage one specimens..................................................................................... 123

Table 8.6 - Stage two specimens..................................................................................... 129

Table 8.7 - Stage three specimens................................................................................... 131

B1. - Water level changes – second experiment – stage one. ......................................... 216

B2. - Water volume changes – second experiment – stage one...................................... 217

B3. - Water level changes – second experiment – stage two.......................................... 218

B4. - Water volume changes – second experiment - stage two. ..................................... 218

B5. - Water volume losses – second experiment – stage three....................................... 219

C1. - Waterstop-RX 101TRH - specimen one. ............................................................... 219

C2. - Waterstop-RX 101TRH - specimen two................................................................ 219

C3. - Waterstop-RX 101TRH - specimen three.............................................................. 220

C4. - Waterstop-RX 101TRH - averages........................................................................ 220

C5. - MC-2010MN – specimen one................................................................................ 221

C6. - MC-2010MN – specimen two. .............................................................................. 221

C7. - MC-2010MN – specimen three. ............................................................................ 222

C8. - MC-2010MN – averages........................................................................................ 223

C9. - Synko-Flex – specimen one................................................................................... 224

C10. - Synko-Flex – specimen two................................................................................. 225

C11. - Sykno-Flex – specimen three............................................................................... 225

C12. - Synko-Flex – averages......................................................................................... 226

ix

LIST OF FIGURES

Figure 2.1 - Concrete Time Dependant Strains ............................................................... 13

Figure 2.2 - Compressive Strength vs Creep Coefficient (Persson) ................................. 27

Figure 3.1 - Gypsum Cylinder End Cap ........................................................................... 41

Figure 3.2 - CAD Drawing of Creep Frames................................................................... 42

Figure 3.3 – Creep Frame ................................................................................................. 43

Figure 3.4 - Creep Frame Compression Springs............................................................... 44

Figure 3.5 - Plate Dimensions........................................................................................... 45

Figure 4.1 – Specific Creep Comparison – Estimated Strain Results to 5-Years............. 62

Figure 4.2 - LVM Mix Design Strain ............................................................................... 65

Figure 4.3 – WJE Inc. Mix Design Strain......................................................................... 65

Figure 4.4 – 5% Metakaolin Mix Design Strain............................................................... 66

Figure 4.5 – 10% Metakaolin Mix Design Strain............................................................. 66

Figure 4.6 – LVM (#2) Mix Design Strain....................................................................... 67

Figure 4.7 – LVM Mix w/ Caltite Waterproofing Admixture Mix Design Strain ........... 67

Figure 4.8 – Caltite Mix Design Strain............................................................................. 68

Figure 4.9 – Long Term Shrinkage Strains, Extrapolated from 28-day Data................... 71

Figure 4.10 – 28-Day Compressive Strength.................................................................... 74

Figure 7.1 - Test configuration (after Dusenberry et al. 1993)......................................... 91

Figure 7.2 - Leakage test setup (after Rashed et al. 2000)................................................ 92

Figure 7.3 - Cross-section of testing experiment (after Clear 1985). ............................... 94

Figure 7.4 - Test setup for water penetration test (after Tan et al. 1996). ........................ 95

x

Figure 8.1 - Keyway dimensions in field (after Hood Canal Retrofit and East-half

Replacment Construction Plans: SEC C-C)............................................................ 106

Figure 8.2 - Test specimen dimensions........................................................................... 107

Figure 8.3 - Dimension specifications for the steel plates. ............................................. 108

Figure 8.4 - Steel Bars 7/8in diameter screwed into bottom plate.................................. 109

Figure 8.5 - Construction setup for initial concrete pour................................................ 110

Figure 8.6 - Completed keyway of initial pour............................................................... 111

Figure 8.7 - Completed test specimens........................................................................... 112

Figure 8.8 - Hydraulic cylinder setup for post-tensioning the specimens. ..................... 113

Figure 8.9 - Waterstop placement within construction joint of specimen. ..................... 116

Figure 8.10 - Tegraproof coating placed on exterior joint face. ..................................... 117

Figure 8.11 - Mortar/slurry grout over initial two-inch depth of the second pour.......... 118

Figure 8.12 - Exposed aggregate along surface of joint caused by Preco HI-V............. 119

Figure 8.13 - Experimental setup of the first experiment. .............................................. 124

Figure 8.14 - Specimen connection to pressure system.................................................. 125

Figure 8.15 - Water collection system located beneath specimens. ............................... 126

Figure 8.16 - Experimental setup of the second experiment. ......................................... 133

Figure 8.17 - Connection of clear plastic tubing to galvanized pipe. ............................. 134

Figure 8.18 - Pressure regulator for air pressure system. ............................................... 135

Figure 8.19 - Concrete filler and sealant applied to the construction joint of stage three

specimens................................................................................................................ 136

Figure 8.20 - Testing setup of the third experiment........................................................ 138

xi

Figure 9.1 - Water volume changes versus air pressure applied to stage one specimens of

the second experiment............................................................................................. 143

Figure 9.2 - Water volume changes versus total pressure on the system for stage one

specimens of the second experiment....................................................................... 144

Figure 9.3 - Water volume changes versus air pressure for the three specimens of stages

one and two that experienced no leakage from the pressure system. ..................... 147

Figure 9.4 - Water volumes lost versus time for the stage three specimens tested......... 151

Figure 9.5 - Total water volume lost at a given air pressure for stage three specimens

immediately before air pressure was increased. ..................................................... 152

Figure 9.6 - Expansion rates of Waterstop-RX 101TRH samples in the third experiment.

................................................................................................................................. 154

Figure 9.7 - Expansion rates of MC-2010MN samples in the third experiment............. 155

Figure 9.8 - Expansion rates of Synko-flex waterstop samples in the third experiment. 156

Figure 9.9 - Average expansion rates of the three waterstops tested in the third

experiment............................................................................................................... 157

Figure 9.10 - Average thickness increases of waterstop samples in the third experiment.

................................................................................................................................. 158

1

SUMMARY

Floating bridge concrete must be watertight, durable, workable, and must have sufficient

cohesiveness to prevent segregation in heavily congested deep walls. The mix design must

experience minimal creep and shrinkage to reduce prestress losses, and shrinkage cracking. As a

result of recent concrete research, new mixes were created incorporating various quantities of fly

ash, silica fume, metakaolin, poly-carboxylate ether superplasticizers, and Caltite waterproofing

admixture. This research focuses on concrete with a water binder ratio of 0.33 and a slump in the

range of 8 to 9 inches. Workability characteristics of the fresh concrete are analyzed and

hardened concrete properties tested in this research are compressive strength, chloride ion

permeability, and creep and drying shrinkage properties.

It was found that metakaolin was successful in producing mix designs with similar

properties as Silica fume modified concrete. Satisfactory strength was achieved through

increasing the fly ash and lowering the silica fume contents, though, chloride ion permeability

was negatively affected. The removal of silica fume and the inclusion of Caltite decreased the

concrete’s resistance to chloride ion permeability and produced concrete that failed to attain the

required 28-day ultimate compressive strength of 6500 psi.

The second part of this study focuses on developing an experimental setup to evaluate

products and construction methods to help prevent water leakage through construction joints in

pontoon floating bridges. A pressure system was used to apply significant pressures to concrete

test specimens containing a construction joint. Different products and construction methods were

used in constructing the joints to determine the most effective methods for preventing water

penetration in the field.

The testing results have shown compaction effort is the most important factor in water

leakage through a joint. Increased compaction in laboratory specimens leads to less water

leakage through construction joints. Product selection was ineffective in preventing water

leakage if concrete compaction was inadequate.

2

CHAPTER 1: INTRODUCTION

1.1 BACKGROUND

The State of Washington has been designing and building concrete floating bridges

since 1938. The original Lacey V. Murrow floating bridge opened to traffic in 1940, and

was considered at that time to be one of the most innovative and controversial bridges in

the world (Lwin el al. 1994). Since that time, Washington State has become a worldwide

authority in the design and implementation of this practical and economically viable

structure. Four floating bridges are currently in service in the state including the new

Lacey V. Murrow Bridge, the Evergreen Point Floating Bridge (or the Second Lake

Washington Bridge), the Third Lake Washington Bridge, and the Hood Canal Floating

Bridge.

The most recent of the floating bridges constructed in Washington is the new Lacey

V. Murrow Floating Bridge. During the design phase of this bridge, extensive research

was performed to determine a mix design that would deliver superior performance for the

demands that the structure would experience. The concrete was developed and named

the LVM mix design, representing the bridge in which it was first used, the Lacey V.

Murrow.

The Hood Canal Floating Bridge was originally constructed in 1961 as a vital link

between the Olympic Peninsula and the central Puget Sound region. On February 13,

1979, the bridge was subject to its 100-year design storm and the West half was unable to

withstand the forces induced by the storm; the West half of the bridge was destroyed and

sank. Following this structural failure, the West half was rebuilt and the East half was

rehabilitated to maintain this important structure for the years to come. Currently, the

3

East half of the Hood Canal Floating Bridge is nearing the end of its design life and

scheduled for replacement

1.2 PROBLEM STATEMENT

It is the desire of the Washington State Department of Transportation to use a state

of the art concrete mix design for the floating pontoon sections of the new Hood Canal

Floating Bridge. The LVM mix design has worked well in the past, but there is room for

improvements, which are discussed in detail in the forthcoming pages.

Concrete, similar to most construction materials, deforms under constant load

sustained for a long period. This deformation is known as creep deflection and must be

understood and accounted for in structural design. One main area of impact that creep

has within concrete structures, and in particular prestressed concrete structures, is loss of

prestressing force due to the shortening of the concrete member.

Concrete is very strong in compression resistance, but weak in tension and must be

reinforced with steel. Prestressing is done for the basic purpose of dramatically reducing

or eliminating the tensile force that the concrete member will have to resist during its

design life. The compressive force that is induced into the concrete member through

prestressing is a moderately high, sustained load and, therefore, has the potential to cause

the concrete to creep. When the concrete member length is shortened, the length of the

elastically strained, tensioned cable is shortened as well, reducing the strain in the cable,

and thus reducing the tensile stress. This reduction in tensile stress in the cable translates

to a reduction in compressive stress in the concrete member, which in turn, causes a

stress reversal in the “tensile zone” of that member. If the stress reversal is large, the

4

concrete must resist the tensile force. Tensile forces in the concrete cause cracks to form

and if the cracks become too dramatic, failure would become eminent.

Floating bridges designers throughout Washington State utilize this prestressing

technique to create floating concrete pontoons. These pontoons are essentially hollow,

concrete beams resting on an elastic foundation. The pontoons used as the floating

structure in the Hood Canal floating bridge are 360 feet long, 18 feet high and 60 feet

wide. The length of a pontoon is subdivided into three rows of 14 cells each, with

outside wall and floor thickness between 8 and 12 inches. These pontoons float due to

the buoyant force of the water, and it must be noted that the air filled cells are key to the

equation of equilibrium. With the pontoons being constructed of concrete that has been

prestressed, creep of the concrete will occur. If the concrete creep is not controlled and

prestress loss occurs, cracks can form in the “tensile zones” of these beams. The tensile

zone is generally on the bottom face of the pontoons, as is usually the case with

supporting beams. Tensile zones are also on either of the sides of the pontoon, depending

on the direction of the dynamic forces induced by wind and wave action. If the tensile

stresses are large enough so that the concrete has to resist a portion of it, the concrete may

crack due to its inadequacy in this application. The cracked concrete would allow water

passage into the air filled cells, which will result in undermining the buoyancy of the

structure. Creep must be minimized so that prestress loss is controlled.

Shrinkage must also be analyzed in concrete used for floating bridges. Shrinkage

in concrete can cause large internal stresses in the concrete matrix and which can lead to

cracking. These cracks are passageways for water to penetrate the outer walls of the

pontoons and enter into the cells. Also, the concrete bridge pontoons have differing wall

5

and floor thickness. This difference in thickness can lead to localized stresses due to

shrinkage and lead to differential shrinkage cracking, and thus, allowing water to enter

the pontoon cells. A concrete of low shrinkage potential is necessary for its use in

floating bridges.

The Hood Canal is a body of salt water that is highly corrosive. Care must be taken

such that structural steel is protected. Included in this list of critical steel members are

steel reinforcing bars and steel prestressing tendons within the concrete pontoons. The

chloride ion penetrability of concrete mixes to be used in floating bridges must be tested.

Water leakage through joints in the pontoons of floating bridges has been a

problem in previous pontoon construction projects. Water trapped within pontoons can

cause excessive damage that if left unchecked can lead to pontoon failure. This water

leakage occurs mainly during or immediately after construction of the pontoon causing a

need for expensive post-construction repairs. Currently pontoon joint leakage is halted

through repairs to the inner surface of the pontoons such as through the use of sealing or

epoxy injection after completion.

Research has been performed in the past to improve mix designs for floating

bridges. The new mix designs have improved workability, durability and limit concrete

permeability. Little research has been performed on construction joint improvements.

Construction joint improvements are needed in pontoon floating bridges to reduce water

leakage and thereby reduce maintenance costs while lengthening pontoon service life.

6

1.3 OBJECTIVES

The overall goals of this research are to improve the concrete mix design currently

used in concrete floating bridges and to develop a watertight construction joint for these

bridges. The LVM mix design is used as a baseline for the development of new mix

designs suitable for use in concrete floating bridges. The intent is to explore new

concrete technology and new materials that have emerged since the LVM creation in

1990, and to implement these into LVM alterations. Tests will be performed to

determine properties in each mix and the results will be compared to the performance of

the LVM. Conclusions will be formulated based on these results.

Some concrete properties are of primary importance in selecting a mix design for

use in concrete floating bridges. These properties include fresh concrete workability,

creep, shrinkage, compressive strength, and chloride permeability. Creep of concrete will

be discussed in detail due to the relatively rare implementation of this test into mix design

performance studies.

Research objectives for the study of watertight construction joints include:

1. To investigate different alternatives for developing a watertight construction joint

suitable for floating bridge pontoons.

2. To design a laboratory experiment to simulate water infiltration in concrete

pontoon joints under conditions similar to those experienced in the field.

3. To recommend guidelines for reducing water penetration through a construction

joint to be included in specifications for future floating bridges and other similar

projects.

7

1.4 TASK SUMMARY

This research consisted of six tasks grouped in two phases described below.

Phase 1 – Review and Development

Task 1: Literature Review, Broad Scope

Collect and review relevant literature, mix design specifications, materials, new or

existing products, research findings and current practices used to produce durable

concrete for submerged concrete structures. Also, collect information relevant to

construction joints in submerged concrete structures. The review will focus on current

construction practices for a floating bridge; mix designs used and new or existing

products for sealing construction joints.

Task 2: Literature Review, Concentrated

Utilize the information obtained after the construction of the last floating bridge in

the early 90’s and other recent knowledge to develop new and improved mix designs.

The improvements would be based on high performance concrete (HPC) properties

especially chloride permeability, compressive strength, creep and shrinkage, and self-

consolidation.

Task 3: Review Synthesis

Based on the information gathered in tasks 1 and 2, identify and discuss material

properties, mix proportions and other factors that affect the durability of concrete in a salt

water environment. Also, based on information from manufacturers and product vendors,

a product’s ability to meet the design needs determined during task 1 is quantified.

8

Products are chosen for laboratory testing to determine their ability to reduce water

leakage through a construction joint.

Task 4: Research Development

Develop a detailed experimental work plan to investigate the influence of the

modifications in the mix design on the strength, durability, and long-term properties of

the concrete. In this task, a work plan to determine the effectiveness of different products

at reducing water penetration through the joint is also developed. The work plan will

include specimen dimensions, the design and construction of a water pressure system and

a testing procedure for determining the necessary requirements for passing the tests.

Phase 2 – Realization and Analysis

Task 5: Implementation

Conduct concrete tests including compressive strength, chloride ion permeability,

creep and shrinkage to determine the influence of any modifications to the mix design

performance. This task also includes performing the experiments developed in task three

to determine product effectiveness at preventing water penetration through the joint. The

data gathered from the experiments will be analyzed to determine the most effective

product or construction method for use in the field.

Task 6: Production

The final report documenting research procedure and findings is provided. This

report will include the following: a synthesis of all pertinent literature from Tasks 1 and

2; a detailed documentation of the experimental work plan: materials used, number of

specimens and testing procedures; a statistical analysis of the testing results; proposed

9

methods for improving the performance of the mix design. The final task also involves

developing a set of construction joint procedures or guidelines to be included in the

specifications for the Hood Canal Floating Bridge East Half Replacement Project. The

guidelines will list a set of construction procedures or product guidelines for reducing

water penetration at the joint.

This report is split into two parts. The first part focuses on the concrete mix design

research to improve the LVM and includes Chapters 2 through 5. The second part

focuses on the construction joint research and includes Chapters 6 through 9.

10

CHAPTER 2: LITERATURE REVIEW

This literature review focuses on the key aspects of concrete mix design

development and performance for use in concrete floating bridges. Topics of interest for

this research were a previous floating bridge mix design study and mechanisms of

concrete creep. Other noted literature included admixture and supplementary

cementitious material effects on freshly mixed and hardened concrete properties.

2.1 CONCRETE FOR THE LACEY V. MURROW FLOATING BRIDGE

Concrete for the Lacey V. Murrow floating bridge was first developed with water

tightness and durability of the concrete as the prime importance. The research committee

conducted a concrete mix development program consisting of three phases. The first

phase included the investigation of many trial mixes. These mixes were used to verify

the resulting concrete properties produced by the inclusion of different supplementary

cementitious materials and concrete admixtures. Silica fume was found to reduce

permeability, increase early compressive strengths, reduce bleeding, and increase the heat

of hydration. Fly ash was found to increased workability, reduce heat of hydration, and

increase ultimate compressive strengths of the concrete. Retarders added to the mixes

increased workability, extended slump life, and improved concrete set control.

Superplasticizers increased workability and decreased the water demand for concrete

mixes.

The second phase of the research was to develop the mix design to be used in the

11

Lacey V. Murrow floating bridge. This was done based on the results from the first

phase. Watertightness, durability, constructability, and compressive strengths were the

key properties that were tested in selecting an appropriate mix design. The third stage

involved constructing full size test sections to test the constructability of the concrete

mix. Wall and slab sections were built and the mix design was evaluated for

effectiveness for the particular application of floating bridges.

The general mix design was created using the three phases for research. WSDOT

and fellow researchers set minimum and maximum quantity extents on different concrete

constituent proportions to be used in the contractor specified mix design. Proportions

selected by the project contractor and approved for use were as follows:

Portland cement type II: 624 lb

Silica Fume* (AASHTO M307): 50 lb

Fly Ash Class F (AASHTO M295): 100 lb

Paving Sand (WSDOT Class 1): 1,295 lb

Coarse Aggregate** (3/8 inch max agg.): 1,770 lb

Water: 225 lb

Water Reducer (ASTM C494, type A or D): 965 mL (25 oz)

Superplasticizer (ASTM C494, type F or G): 5065 mL (131 oz)

Air Entrainment: none

Water/Cementitious Material ratio: 0.33

Slump: 7 in.

*- Silica Fume slurry – 45% Silica fume solids, water and a small amount

of superplasticizer

**- Gradation similar to that of ½ inch coarse aggregate

12

2.2 CREEP OF CONCRETE

Creep is defined by a deformation occurring under, and induced by, a constant

sustained stress. Creep strains are considered proportional to the applied stress for stress

values below 0.40*f’c (Carriera et.al. 2000). According to the Portland Cement

Association, the amount of creep is dependant upon the magnitude of the applied stress,

the age and strength of the concrete when the stress is applied, and the length of time the

concrete is stressed. Other factors that affect the creep potential of concrete have to do

with the quality of the concrete and the conditions of exposure. These factors include:

type, amount and maximum size of aggregate; type of cementitious materials; amount of

cement paste; volume to surface ratio of the concrete element; amount of steel

reinforcement; curing conditions prior to the load application; and the ambient

temperature and humidity (Design and Control of Concrete Mixtures, PCA, p269).

A paper by Dilger and Wang (2000) provided definitions of creep terminology.

Basic creep is the creep without moisture exchange between the concrete and the ambient

environment. Drying creep is the additional creep caused by drying, i.e. by the loss of

moisture to the environment. Total creep of the concrete exposed to the environment is

the sum of basic and drying creep. The quantities defined here can be seen graphically in

Figure 2.1. The statement was made that high performance concrete (HPC) behaves

differently than normal strength concrete and therefore, property characteristics are

different with time. The current prediction models in codes and practice at the time this

paper was written did not apply to HPC. New creep prediction model equations are

provided in this paper for the use with high performance concrete.

13

Time (t-t0)

Strain

t0

Drying

Creep

Total

Creep

Initial

Elastic

Strain

Shrinkage

Basic

Creep

Figure 2.1 - Concrete Time Dependant Strains

In the book Creep of Plain and Structural Concrete, Neville, Dilger and Brooks

(1983) asserted that the deformation characteristics of a material are a critical element in

the knowledge of their behavior and an essential feature of their properties. The authors

insisted that creep deformation could be substantial and must be taken into account in

addition to initial elastic strain. This is demonstrated by sited test results showing creep

strains after one year of load as high as 2 to 3 times that of the initial elastic strains. A

fundamental generalization was made claiming hydrated cement paste is the seat of

concrete creep. This statement has been verified by tests cited in this book researching

creep of concrete with varying degrees of hydration.

14

Brooks and Neville (1975) studied concrete creep with the intent developing

extrapolation equations to estimate long-term creep from short-term tests. They

determined that creep and shrinkage at one year could be predicted from measured values

at between seven and 28 days by means of linear and power equations. From their

research, conclusions were made that creep tests of approximately 100 days can be used

to very accurately predict the values at 1 year with an acceptable error coefficient. They

surmised that 1-year deformation, measured in microstrain, could be predicted from

experimentally determined 28-day values by the use of the following equations:

• basic creep: c

365

=6.0+1.59c

28

• total creep: c

365

=18.4+1.70c

28

and further extrapolated to:

or

)(45.1

45.15

)(15.1

4.57

365

6.0

365

Meyersc

t

c

Rossc

t

c

t

>−













+

=

>−













+

=

with an error coefficient of :

(

)

n

cc

c

M

t

2

1

−

= c=actual creep after 1 year

c

t

=predicted creep after t days

n=number of tests

15

Brooks and Neville (1978) wrote a second paper with the intent of verifying or

altering their previous prediction equations using a larger database of creep test results.

The equations in this paper are based on 5-year creep data. The equations are provided to

predict creep and shrinkage at any age up to 5 years from values determined

experimentally at 28 days, within quoted accuracies. It should be noted that these

equations are different from those previously published. The results are statistically

based on a 95% confidence interval. The relationships are sensibly independent of mix

properties, type of aggregate, size of specimen and age at testing. The expressions

provided in this paper are as follows:

basic creep- c

t

=c

28

*0.50t

0.21

; M

bc

=16%

total creep- c

t

=c

28

[-6.19+2.15ln(t-t

28

)]

1/2.64

; M

tc

=19%

shrinkage- ε

sh

(t,t

sh,0

) = A′(ε

sh28

)

a′

; M

sh

=14%

where A′ = [1.53log

e

(t-t

sh,0

)-4.17]

2

and

)(log2.2990.2

100

0,she

tt

a

−+

=

′

Brooks and Neville noted that improved prediction accuracies can be obtained by

increasing the duration of the short-term test, but testing costs increase with test

continuance. The required accuracy for the particular application must be assessed so

that appropriate creep test duration can be determined.

2.2.1 CREEP AFFECTED BY CONCRETE COMPOSITION

Zia (1993) made generalizations about concrete creep in High Performance

Concrete, A State of the Art Report. These are similar to the generalizations that can be

16

made about shrinkage of concrete. Main points included were: when the water to cement

ratio is increased, the creep potential of the concrete is increased; when the cement

content is increased, the creep potential of the concrete is increased; with an increase in

aggregate content and stiffness, creep is decreased due to the restraining action of the

aggregate.

Collins (1989) studied high strength concrete mixes with compressive strengths

between 8,700 and 9,300 psi were tested. Test results of the different mix designs

showed that creep was less for concrete mixes with lower cement paste content and larger

aggregate. The tests also showed that creep was not significantly affected by the

inclusion of a high range water reducer into the mix design.

Carrette, Bilodeau, Chevrier, and Malhotra (1993) tested high performance

concretes with high volumes of fly ash. Concrete mixes had excellent mechanical

properties with relatively low levels of creep deformation.

Zia (1993) researched high strength concretes with different aggregate types

including crushed granite, marine marl, and rounded gravel were evaluated for creep

deformation. These high strength concretes, with compressive strengths exceeding

10,000 psi, showed creep strains ranging from 20% - 50% of that of ordinary concrete.

The concrete consisting of marine marl aggregate had a much higher specific creep than

that of either the crushed granite of the rounded gravel concretes.

17

The forth chapter of a book by Neville, Dilger, and Brooks (1983) discussed the

influence of aggregate on creep. The authors’ findings based on prior research was that it

is acceptable to assume that the maximum size and grading of aggregate do not affect

creep given that full compaction within the concrete has been achieved.

Brooks (1999) assessed the affects of admixtures and supplementary cementitious

materials by a relative deformation approach. This was done by comparing the

deformation of the admixture concrete with that of the control concrete having the same

mix proportions by mass, with ultimate values for creep obtained by extrapolation.

Various chemical admixtures were tested and it was determined that no

significant differences in creep strain occurred between types of plasticizers and

superplasticizers. However, a general increase in creep of 20% was shown, as compared

with the control concrete having the same mix proportions (σ=23%). The likely reason

for this increase is thought to be the chemical admixture ability to entrain air, which in

turn makes the hardened cement paste weaker. However, a point of note is that this

increase of 20% is conflicting within the article and may be a decrease of 20%. This

should be investigated further to determine the correct finding.

Blast furnace slag, fly ash, and silica fume, were used as supplementary

cementitious materials in the test mixes in this paper as well. The inclusion of blast

furnace slag (BFS) showed a decrease of average ultimate creep with an increase of

replacement of cement with slag. Shrinkage of the concrete was unaffected by the

increase in slag content. It was also shown that with BFS, lower creep values were

associated with slower development of strength. Fly ash concrete was shown to have

18

reduced average ultimate creep values with an increase of the cement replacement

percentage with fly ash. This trend was explained by looking at the concrete strength

development: fly ash concrete continues to develop strength through a very long

hydration process. As was the case with BFS, shrinkage was unaffected by the use of fly

ash in the concrete mix. A small reduction in creep was shown for small quantities of

cement replacement with silica fume. Creep increases with silica fume replacement of

over 16% of ordinary Portland cement.

Brooks and Neville (1992) published findings for creep deformations determined

first hand as well as findings published by other researchers. The results were

summarized into effects of different admixtures and different supplementary cementitious

materials separately. Water reducers showed a very wide range of effects on concrete

creep. Results of various tests ranged from 34% to 166% of creep strain, as compared to

a reference mix. However, water reducers created from different chemical bases showed

differing results. Lignosulphonate admixtures lead to a higher basic creep than

carboxylic acid admixtures. Carboxylic acid admixtures often result in a reduction in

basic creep compared with plain concrete. No consistent trend for concrete creep can be

observed when there is a change in cement paste content, in the type of aggregate, or in

cement composition.

There have been no publications regarding retarding admixtures (ASTM C494-82

type B) and their effect on concrete creep. Calcium chloride used as an accelerator has

been shown to increase creep in the range of 122% to 136%. Lignosulphonate /

triethanolamine based accelerators increased basic creep in the range of 110% to 125%

19

and affected total creep (under drying conditions) in the range of 92% to 135%. A wide

variation of relative deformations have been shown for superplasticizer inclusion in

concrete mixes, however, an increase in concrete creep is the general trend.

Fly ash, blast furnace slag, and silica fume were the supplementary cementitious

materials reviewed in this paper. Fly ash concrete has shown reduced creep values for up

to 35% ordinary Portland cement replacement. Reduced creep values have been shown

for blast furnace slag with replacement quantities of up to 75% of ordinary Portland

cement. With 30% of ordinary Portland cement replaced by silica fume and various

water cement ratios, approximately 50% more creep was observed under drying

conditions after moist curing. Less basic creep was observed for the silica fume concrete

if the concrete was autoclaved, but more basic creep occurred after moist curing.

Brooks (2000) reviewed different admixtures and supplementary cementitious

materials for their effect on concrete creep. Lignosulphonate and carboxylic acid water

reducers both result in greater mean deformations, however the results were not very

different between the two admixtures or their respective control concretes. Sulfonated

melamine formaldehyde condensates (SMFC), sulfonated naphthalene formaldehyde

condensates (SNFC), and copolymers used as superplasticizers all showed a general

increase in the mean creep deformation compared with plain concrete. However, the

basic creep of concrete with the copolymer admixture was not significantly different from

that of plain concrete. Ground granulated blast furnace slag (GGBFS) tended to decrease

total creep as the slag levels increase in the concrete mix, but only for low water cement

ratios. For higher water cement ratios, creep appears to increase. It has been determined

20

that fly ash inclusion into concrete mixes reduces basic creep. Silica fume used as a

supplementary cementitious material increases basic creep as the silica fume content

increases. However, total creep decreases for low levels of silica fume. Autoclaved

concrete showed a large reduction in creep at high levels of silica fume addition, up to

about 30%. Relationship equations were included in this article to estimate creep based

on the replacement percentages of ordinary Portland cement with the supplementary

cementitious materials.

Based on the results of this research, Table 2.1 was created and included in the

article showing the general influence trends that the admixtures and supplementary

materials have on concrete creep. The variable R in the table stands for replacement

percentage

Table 2.1 - Trends in Concrete Creep

Ingredient

Basic

Total

Plasticizers/

Superplasticizers

decrease with No

increase of R Change

decrease with decrease for

increase of R R>=10%

increase with R>7.5% increase with R>15%

no change for R<7.5%

decrease for R<15%

Silica Fume

Fly Ash

Blast Furnace Slag

Creep at constant stress-strength ratio

increase by 20% increase by 20%

.

Khatri (1995) studied a concrete mix with water to cementitious material ratio of

.35, and a constant binder content of 430 kg/m

3

. Results of this study showed that silica

fume at about 10% replacement marginally decreased the workability of the concrete but

significantly improved the mechanical properties. These improvements included a

21

decrease in creep at all ages and refined pore size, which increases the concrete

compressive strength. The strain due to creep was said to be caused by the removal of

adsorbed water. When silica fume was added to high slag concrete, the creep was not

affected. When a ternary mixture, or one with three cementitious materials, was created

containing fly ash, general-purpose cement, and silica fume, strain due to creep was

increased.

A study performed by Jianyong and Yan (2001) was a comparison of the creep of

different materials used as concrete binders. The materials of interest included ordinary

Portland cement (OPC), ultra fine ground granulated blast furnace slag (GGBS), and

silica fume (SF). The creep tests were performed at a temperature of 20±3°C, with a

testing duration of 180 days, and the test cylinders were loaded at 40% of their respective

28 day compressive strength. For comparison, drying shrinkage specimens were studied

simultaneously in the same environmental conditions as the loaded creep specimens. The

strains due to creep and shrinkage were measured using a mechanical comparator. In this

study, replacing OPC with 30% (by weight) GGBS and 10% (by weight) SF delivered the

best results for creep strain. The proportions of material for this mix was 360 kg/m

3

OPC, 180 kg/m

3

GGBS, 60 kg/m

3

SF, and 156 kg/m

3

of water, producing a water to

cementitious material ratio of 0.26.

The mineral and chemical admixtures examined in the study by Memon, Radin,

Zain and Trothier (2002) included fly ash, ground granulated blast furnace slag, silica

fume, and superplasticizers. Blended mixtures, or a combination of the mineral and

22

chemical admixtures, performed better in strength and showed a general result of lower

permeability. This result was achieved by greater pore refinement due to the better

distribution of particle sizes in the blended mixes.

Ramachandran (1995) discussed concrete creep in the Concrete Admixtures

Handbook for various reasons having to do with the causes and effects that mix design

and proportioning have on the creep potential of the concrete. Summaries of the author’s

conclusions based on previous studies are divided into admixture categories below.

• Accelerators

Based on previous tests, calcium chloride and triethanolamine admixtures

increase the creep of concrete. With 1.5% CaCl

2

addition, the percentage increase in

creep of the concrete cylinders loaded at 7 and 28 days was 36% and 22 % respectively.

Creep was increased by triethanolamine only at early age loading (7 days) when

lignosulfonate was added to the concrete as well. Calcium formate addition tends to

increase shrinkage.

• Water reducers / Retarders

Listed in this section of the book were several of the basic causes of concrete

creep. Factors listed were type of cement, mix composition, type of cement, age at

loading, degree of hydration at loading, incremental hydration under loading, moisture

loss from concrete under sustained load, and movement of moisture in the cement gel

under conditions of hygral equilibrium between the ambient medium and the concrete.

Studies have shown that lignosulfonate admixtures increase the rate and total creep for

concrete with type I cement but there is no significant effect with type V cement. The

23

rates and formation changes of the hydration process caused by water reducers and

retarders altars the creep potential of a concrete when loaded at different times or ages

with a sustained load. Hydroxycarboxylic acid based water reducers/retarders tend to

increase long term creep except for lightweight concrete, however the initial creep rate is

low. The claims were made that in general, water reducers have either no effect or they

increase the creep of concrete and retarders increase the creep of concrete.

• Superplasticizers

The author of this section observed that superplasticizers generally decrease

shrinkage of concrete, though exceptions do occur. The general consensus is that the

addition of superplasticizers into a mix results in approximately the same creep as the

reference mix. In on instance, an identical mix design was altered three times by adding

one different chemical superplasticizer at a time. The superplasticizer based on

melamine added into the mix decreased creep, one based on napthalene showed

approximately the same creep as the reference and one based on Lignosulphonate

increased the creep of the concrete mix.

• Air Entrainment

The use of air entrainment is not permitted in the LVM concrete mix and is not an

important factor for the creep of concrete.

• Polymer modified Concrete

In general the use of polymers to modify a concrete mix design leads to large

creep deformations. Catastrophic failures of the concrete occur at 50°C

• Mineral Admixtures

24

The mineral admixtures of interest in this book are fly ash and silica fume, and are

used as supplementary cementitious materials. A study showed that fly ash type F with

replacement values of up to 15% of the ordinary Portland cement, the creep remains the

same. When more than 15% of the OPC by weight is replaced by fly ash type F, the

creep is slightly higher. High strength concretes containing silica fume were shown to

have significantly less creep than normal strength concretes due to the fact that SF

accelerates the strength development of the concrete. The general trend of concrete is

that as compressive strength of the concrete increases, the creep potential of the concrete

decreases.

2.2.2 CREEP RELATED TO COMPRESSIVE STRENGTH AND SHRINKAGE

Zia (1993) reported a trend in concrete creep that for higher strength concrete,

creep potential is lower. Another important trend is that creep deformations are similar

for silica fume concrete, fly ash concrete, and ordinary Portland cement concrete with

similar compressive strengths.

A study by Paulson, Nilson and Hover (1991) dealt with the long-term deflection

of high strength concrete beams. The study showed that the creep coefficient for high

strength concrete under steady and continuous axial compression was considerably less

than the creep coefficient of ordinary strength concrete.

The research done by Yamamoto (1990) demonstrated that creep deformation of

high strength concrete columns was much less than that of normal strength concrete.

25

Burg and Ost (1994) studied the engineering properties of five high strength

concrete mixes. The concrete had components of no mineral admixtures, silica fume

only, or both fly ash and silica fume in addition to the ordinary Portland cement. The

creep strain was measured under about 39% of f’

c

(at 28 days) for a test duration of 430

days, and then unloaded so that creep recovery was measured. Specific creep was

determined to be the lowest for the concretes with the highest compressive strengths.

This was attributed to the paste composition and internal structure of the concrete.

Specifically, proportions of the mix (per cubic yard) with the lowest creep values were

800 lbs of cement type I, 125 lbs of silica fume, 175 lbs of fly ash, 425 fl oz. of high

range water reducer, 39 fl oz of retarder type D, a water to cement ratio of 0.318 and a

water to cementitious material ratio of 0.231. The value of the specific creep for this mix

was .24 millions of an inch/psi.

Neville, Dilger and Brooks (1983) reviewed research of the influence of stress

strength ratios and concrete age effects on creep. The authors placed the linear

relationship between concrete creep and applied stress from a ratio of about 0 to between

0.30 and 0.75. Above that limit of linearity, creep increases with stress at an increasing

rate. Also determined was that for a given stress strength ratio, creep is the same

regardless of how strength or stress have been altered, as long as their ratio is the same.

When humidity is a variable in research, it can be said that the relation between

creep and stress to strength ratio seems to be approximately the same for different relative

humidity values, provided considerable shrinkage does not occur. For this to occur, the

26

concrete must reach hygral equilibrium with the medium prior to the application of the

load.

Regarding age at application of load, loading older concrete would definitely tend

to decrease creep due to the more mature hydration. After about 28 days, however,

differences are minor since strength gain is very slow at this point and the concrete

hydration is more mature. The creep at this point is only really dependant on the stress to

strength ratio. A section on maturity of concrete was included and the term reflects the

degree of hydration and therefore the amount of cement gel in the concrete matrix. It has

been shown that strength and maturity are not linearly related, and it is the maturity of the

hydration, not the strength of the concrete, that is the fundamental factor of creep.

Persson (2001) performed an experimental and numerical study on the similarities

and differences in mechanical properties of self-compacting concrete (SCC) and normal

compacting concrete (NCC). Properties of interest included strength, elastic modulus,

creep and shrinkage. Eight mix designs were tested with water-cementitious material

ratios ranging from .24 to .80. Four mixes were self-compacting and each of these mixes

had a corresponding normal compacting concrete of similar water-cementitious material

ratio. To increase the viscosity of normal compacting concrete, fillers such as fly ash and

silica were used, in addition to superplasticizer introduction into the mixes. Spring

loading frames were used to perform the creep tests, and parallel specimens were used to

study shrinkage. For creep analysis, four different stress levels were studied including

0.20, 0.40, 0.55, and 0.70. Several conclusions reached as a result of this on going study.

First, the creep, shrinkage and elastic modulus of the two types of concrete corresponded

27

well when the strength was held constant. When the strength loading for the creep tests

was held constant, the creep coefficient of mature concrete was similar between the two

types of concrete. The creep coefficient of concrete increased greatly, when the concrete

was loaded at a young age, though this increase was similar for both types of concrete.

When the compressive strength of the concrete was high, the creep coefficient was

greatly reduced, which is similar to many results from previous literature. A graphical

display of these findings is shown here in Figure 2.2.

Figure 2.2 - Compressive Strength vs Creep Coefficient (Persson)

Zia (1993) surmised that concrete resistant to shrinkage also has low creep

potential.

28

2.3 OTHER CONCRETE MATERIALS AND ADMIXTURES

Metakaolin is a highly effective pozzolanic material that can be used as a

supplementary cementitious material. Brooks and Johari (2001) found that total creep,

basic creep, as well as drying creep were significantly reduced particularly at higher

metakaolin replacement levels. This effect can be attributed to a denser pore structure,

stronger paste matrix, and improved paste aggregate interface of the metakaolin concrete

mixtures. This is a result of the formation of additional hydrate phases from secondary

pozzolanic reaction of metakaolin and its filler effect. The research showed the 200-day

drying creep was reduced for metakaolin concrete at high levels of replacement (15%

ordinary Portland cement replacement). Shrinkage tests showed an increase in total

autogenous shrinkage at the 5% replacement level, but at the higher 10 to 15% levels of

replacement, total autogenous shrinkage was decreased.

Calderone, Gruber and Burg (1994) discussed some general properties of high

reactivity metakaolin (HRM) and its effect on freshly mixed and hardened concrete.

HRM is not an industrial byproduct, as are many other supplementary cementitious

materials. HRM is specifically manufactured for its particular uses, is nearly 100%

reactive, and conforms to ASTM C618, class N pozzolan specifications. This study

compares the relative performance of five mixtures produced with HRM and silica fume

at various contents including two mixes with HRM, 5% and 10% replacement, two mixes

with silica fume, 5% and 10% replacement, and one control mix with neither HRM nor

silica fume. The required additions for high range water reducer (HRWR) are 25% to

29

35% less for mixes containing HRM than for the mixes containing SF to obtain similar

slumps. The HRM mixes were also less sticky and provided similar set times to that of

SF concrete. The HRM concretes had higher compressive strengths, lower chloride ion

penetration, and similar drying shrinkage to the SF concrete with values for 28-day

shrinkage of 280 microstrain for the metakaolin concrete and 260 microstrain for the

silica fume concrete. The values for shrinkage for the two mixes were equal after 156

days of drying. HRM used in powder form was in some cases better than the SF in slurry

form.

The conclusions of a study by Ding and Li (2002) were that metakaolin is

comparable to silica fume as a supplementary cementitious material, but is lower in price.

Metakaolin is produced by a well-controlled manufacturing process, and is typically

incorporated into concrete to replace 5-20% by weight of cement. Ding and Li

systematically studied and compared the effects of metakaolin as a cementitious

replacement to those effects of silica fume. Seven mix designs were created using 0, 5,

10, and 15% ordinary cement replacement by metakaolin or silica fume. All of the mixes

had a water to binder ratio of 0.35, a sand to aggregate ratio of 0.40, 1.0% (by weight of

cement) addition of napthalene sulfonate-based superplasticizer, and 0.25% addition of a

set retarder.

All of the metakaolin concrete mixes had much higher slump values than that of the

silica fume concrete mixes, and they showed higher slump values than the control mix at

the 5 and 10% levels. The compressive strength test results indicated that the

introduction of metakaolin into concrete produces much higher strength than the control

30

at all levels, and very similar results to that of the silica fume concrete at the same

replacement levels.

Metakaolin concrete shows a faster initial rate of shrinkage than the control and the

silica fume concrete, but the rate levels off within days and leads to lower values over

time. The results showed lower values for shrinkage for greater levels of replacement of

cement with metakaolin, and the same was true for silica fume. The lowest shrinkage

values observed were from the mix with 15% metakaolin replacement.

The tests for chloride diffusivity showed that metakaolin is less effective than silica

fume at all similar replacement levels, but is still better than the control mix. After 90

days of observation, the 15% replacement levels of metakaolin and silica fume had

equivalent values for chloride diffusivity.

The purpose of a study by Sicker and Huhn (1997) was to characterize the

influence of silica fume and high reactivity metakaolin and of superplasticizers on the

rheological properties of mortars by means of fluidity measurements. New generation

superplasticizers such as polycarboxilic ether based superplasticizers were compared with

the commonly used, older types. The effect of superplasticizers in fresh concrete is a mix

with significantly lower flow resistance, while the viscosity remains almost unchanged.

Thus, the risk of segregation is no greater, as it would be with the addition of water. The

rheological properties of mortars are extremely dependant on the type of superplasticizer

and pozzolans in the mix design. The results of this study indicated that concrete made

with metakaolin and the polycarboxilic ether based superplasticizers had the longest

effective period for good rheological performance.

31

A study by Feng, Chan, He, and Tsang (1997) showed that when 10% of ordinary

Portland cement was replaced by an equal weight of shale ash, the compressive strength

of the concrete increased 5 to 10%. Oil shale ash is an industrial waste product that can

be utilized as a pozzolana and can also be used as a carrier for superplasticizer to form a

carrier-fluidifying agent (CFA). When the shale ash was used as a carrier for the

superplasticizer, the resulting CFA could control slump loss. One such test showed that

when a 1.5% dosage of CFA was used, the slump was maintained for 90 minutes.

Xu and Chung (2000) performed research to show the effects of silica fume as a

supplementary cementitious material in concrete. The research was also to show the

increased benefits of using silane in conjunction with the silica fume. Silica fume was

shown in this paper, and has been shown in applications previously, to have significant

effects on the properties of the resulting concrete mixes. It has also been shown to

degrade the workability of the concrete.

Silane is a concrete additive that can be introduced in two ways: first in the form

of a coating on the silica fume particles, and second in the form of an admixture. Both of

the methods of silane uses were shown to enhance the workability and increase the

strength of the concrete. The method of coating the silica fume with silane was shown to

be the better method in terms of mechanical properties; however, this method is more

difficult to perform in the mixing process. There was no data recorded for creep effects

but the results for shrinkage in the concrete containing silane and silica fume showed an

improvement over the concrete mixes with no silane.

32

CHAPTER 3: EXPERIMENTAL METHODS

3.1 MATERIALS AND MIX DESIGNS

Concrete used in floating bridges must be designed with compressive strength,

durability, and long-term properties as the critical factors for successful performance.

The LVM mix design, of which the origin was previously described in detail, has these

characteristics and was used as the reference mix for use in the development of new mix

designs. The LVM concrete is Mix Design number 1 and Mix Design number 5 in this

research. The concrete constituent quantities are shown in Table 3.1 and Table 3.5.

During the construction of the Lacey V. Murrow floating bridge, Wiss, Janney,

Elstner Associates (WJE), Inc analyzed the suitability of the mix design. Within their

published report (1993), they discussed mix design development, suitability testing

criteria, and the conclusions based on their findings. This report included several

recommendations for future construction of watertight structures. It was stated that mix

alterations could be made such that the silica fume content be reduced to the 4 to 5

percent level and fly ash content be increased to 200 or more pounds per cubic yard.

They anticipated that this change could be made without impairing the permeability of

the concrete and would still maintain the other desirable qualities of the LVM mix. WJE,

Inc recommended that further tests be done to verify this conclusion. This LVM

alteration is labeled WJE, Inc mix design and is mix number 2 in this study. The

quantities can be found in Table3.2.

Based on the findings of the literature review, concrete products were found that

were not used in practice when the LVM mix was first developed. New mix designs

33

were formulated for the purposes of this research based on previous successes of the

relatively new products. Metakaolin is a product that is currently being developed and is

used as a supplementary cementitious material much like silica fume. The report findings

listed in the literature review proved metakaolin to be a viable material for use in

concrete floating bridges. It was also recommended that additional research on this

product would be valuable. Two mixes, one with 5 percent ordinary Portland Cement

(OPC) replacement and one with 10 percent OPC replacement were designed. These

replacement values were selected so that nearly direct comparisons could be made to the

WJE, Inc mix, which was designed with 5 percent OPC replacement with silica fume,

and the LVM mix, which was designed with about 8 percent OPC replacement with silica

fume. The mix designs incorporating metakaolin are numbers 3 and 4 and can be seen in

Table 3.3 and Table 3.4, respectively.

A concrete waterproofing admixture that has been of interest to many developers

is Everdure Caltite. Traditional means of creating a waterproof concrete structure has

been the use of external membranes or surface treatments. As was mentioned previously,

silica fume and metakaolin are also effective in reducing the permeability of concrete, but

in a different way. Caltite was incorporated into two of the mix designs tested in this

study. The first mix utilized the LVM mix design quantities, with some of the mix water

replaced with equal parts of the Everdure Caltite. The replacement quantity was

consistent with the recommended Caltite to concrete ratio or 6 gallons of Caltite for every

cubic yards of concrete. This mix design can be seen in Table 3.6. The second Caltite

mix design, and the final mix incorporated into this study, was studied for its properties,

as the other mixes were, but was intended to be a cost saving mix. The mix design would

34

be the same as the LVM, though it would not contain silica fume. The concrete

quantities for this mix can are shown in Table 3.7. The cementitious material quantity is

slightly less than the LVM parent mix. It was anticipated that this mix design would

produce concrete strength in excess of the required 6500 psi. Workability properties

would be similar to the LVM and the level of chloride ion penetration would be

acceptable as well due to the presence of Caltite. The Caltite quantity was as before, 6

gallons per cubic yard of concrete.

This research necessitated the casting of nine concrete test cylinders for each mix

design to be studied. Seven of the cylinders were standard 6 by 12 inch specimens, and

two of the cylinders were standard 4 by 8 inch specimens. Three of the seven 6 by 12

inch cylinders were needed to obtain an average ultimate compressive strength value for

each mix design. The remaining four cylinders were used for the creep tests: two

cylinders for the total strain measurements and two companion cylinders for the

shrinkage measurements. The two 4 by 8 inch specimens were required for the chloride

ion penetration tests. All the cylinders were cast in vertical, one-time-use plastic molds.

The course and fine aggregate used in the concrete of the LVM floating bridge

had the gradations listed in Table 3.7. Coarse and fine aggregates used in this research

were from Glacier Northwest in Dupont, Washington. This is the anticipated stockpile

that will be used for the actual concrete used in the floating bridge construction and had

gradations very similar to that of the original LVM mix. The quantities were entered into

an aggregate spreadsheet to determine the effectiveness of the gradations and the results

were plotted on a gradation power chart to graphically display the results. The

spreadsheet format can be seen in Table 3.8.

35

The ordinary Portland cement used in the original LVM mix design and required

was OPC Type II. According to the Portland Cement Association, type II Portland

cement generates less heat at a slower rate and has a moderate resistance to sulfate attack.

A lower heat of hydration is beneficial in large structures to avoid shrinkage cracking.

Resistance to sulfate attack in a harsh environment is critical for the durability of

hardened concrete.

As a result of conclusions reached from the literature review, a relatively new

superplasticizer was selected for use in this research. Polycarboxylic-ether based

superplasticizers produce concrete with more desirable concrete workability

characteristics than the older lignosulfonate, naphthalene, or melamine based

superplasticizers. The superplasticizer used in all mixes tested was Glenium 3000.

Based on the effectiveness of this product, it was determined that no normal range water

reducer would be necessary in LVM mix or any of the new mix designs.

36

Table 3.1 – Mix #1 LVM Mix Design, Reference Mix Design

mix proportions

Concrete Constituent

lbs / 1 yd

3

Course Aggregate 1770

Fine Aggregate 1295

Portland Cement Type II 624

Silica Fume (AASHTO M307) 50

Fly Ash (AASHTO M295) 100

Water (Total) 255

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 5.5 floz/cwt

w/c ratio= 0.329

slump = 8.0"

Table 3.2 – Mix #2 1st Alteration - WJE, Inc. Report Recommendation

mix proportions

Concrete Constituent

per 1 yd

3

Course Aggregate 1770 lb

Fine Aggregate 1295

Portland Cement Type II 540

Silica Fume (AASHTO M307) 35

Fly Ash (AASHTO M295) 200

Water (Total) 255

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 4.3floz/cwt

Caltite none

w/c ratio= 0.329

slump = 7.5"

37

Table 3.3 – Mix # 3 - 2nd Alteration - Metakaolin - 5% OPC Replacement

mix proportions

Concrete Constituent

per 1 yd

3

Course Aggregate 1770 lb

Fine Aggregate 1295

Portland Cement Type II 636.3

Silica Fume (AASHTO M307) none

Fly Ash (AASHTO M295) 100

Metakaolin 38.75

Water (Total) 255

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 5.5floz/cwt

Caltite none

w/c ratio= 0.329

slump = 9.0"

Table 3.4 – Mix # 4 - 3rd Alteration - Metakaolin - 10% OPC

Replacement

mix proportions

Concrete Constituent

per 1 yd

3

Course Aggregate 1770 lb

Fine Aggregate 1295

Portland Cement Type II 597.5

Silica Fume (AASHTO M307) none

Fly Ash (AASHTO M295) 100

Metakaolin 77.5

Water (Total) 255

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 7.0floz/cwt

Caltite none

w/c ratio= 0.329

slump = 8.5"

38

Table 3.5 – Mix # 5 - LVM Mix Design #2 - Reference Mix Design

mix proportions

Concrete Constituent

per 1 yd

3

Course Aggregate 1770 lb

Fine Aggregate 1295

Portland Cement Type II 624

Silica Fume (AASHTO M307) 50

Fly Ash (AASHTO M295) 100

Water (Total) 258.66

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 5.5floz/cwt

Caltite none

w/c ratio= 0.334

slump = 8.5"

Table 3.6 – Mix # 6 - 4th Alteration - LVM Mix with Caltite Admixture

mix proportions

Concrete Constituent

per 1 yd

3

Course Aggregate 1770 lb

Fine Aggregate 1295

Portland Cement Type II 624

Silica Fume (AASHTO M307) 50

Fly Ash (AASHTO M295) 100

Water (Total) 222.12

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 5.5floz/cwt

Caltite 6 gallons

w/c ratio= 0.351

slump = 8.5"

39

Table 3.7 – Mix # 7 - 5th Alteration - Caltite Mix Design

mix proportions

Concrete Constituent

per 1 yd

3

Course Aggregate 1770 lb

Fine Aggregate 1295

Portland Cement Type II 624

Silica Fume (AASHTO M307) none

Fly Ash (AASHTO M295) 100

Water (Total) 154.64

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 6.3floz/cwt

Caltite 6 gallons

w/c ratio= 0.282

slump = 9.0"

Table 3.8 - Aggregate Gradations

Course Aggregate

Weight

Sieve Percent Passing

Size Passing (lbs)

5/8 100% 1770

1/2 97.40% 1724

3/8 82.80% 1466

1/4 32.00% 566

#4 5.30% 94

#6 1.00% 18

Total Weight

1770.0

Fine Aggregate

Weight

Sieve Percent Passing

Size Passing (lbs)

#4 97.60% 1264

#8 76.10% 985

#16 55.30% 716

#30 35.60% 461

#50 13.30% 172

#100 2.70% 35

#200 0.70% 9

Total Weight

1295.0

40

Table 3.9 - Total Aggregate Blend Gradation

B L E N D R E Q U I R E D - %

1-1/2" X 3/4"

3/4" X #41/2" X #4

3/8" X #4

Bldg-sand

Pavg-sand

0 0 58 0 42 0 100

ACCUMULATED P E R C E N T P A S S I N G

B L E N D E D

SIEVE SIZE

1-1/2" X 3/4"

3/4" X #41/2" X #4

3/8" X #4

Bldg-sand

Pavg-sand

A G G'S

(us) (mm)

1-1/2" 37.500 100.00 100.00 100.00 100.00 100.00 100.00 100.00

%

1.0" 25.000 100.00 100.00 100.00 100.00 100.00 100.00 100.00

%

3/4" 19.000 100.00 92.10 100.00 100.00 100.00 100.00 100.00

%

1/2" 12.500 100.00 47.20 97.40 100.00 100.00 100.00 98.49 %

3/8" 9.500 100.00 23.50 82.80 89.80 100.00 100.00 90.02 %

#4 4.750 100.00 3.00 5.30 12.90 100.00 99.60 45.07 %

#8 2.360 100.00 0.00 1.00 1.60 91.30 75.00 38.93 %

#16 1.180 100.00 0.00 0.00 0.00 64.50 49.00 27.09 %

#30 0.600 100.00 0.00 0.00 0.00 38.20 31.00 16.04 %

#50 0.300 100.00 0.00 0.00 0.00 18.50 13.00 7.77 %

#100 0.150 100.00 0.00 0.00 0.00 7.70 4.00 3.23 %

#200 0.075 0.00 0.80 0.00 0.30 2.30 1.00 0.97 %

(FM)

0.00 7.34 6.14 5.96 2.80 3.28 4.73

To achieve the standard for end conditions of compressive strength and creep test

cylinders, specimen end grinding, sawing, or capping must be performed. A high-

strength gypsum mortar called Hydrostone was used as an end-capping compound. This

material was obtained from Special Effects Supply Corporation, Salt Lake City, Utah. A

mortar of high compressive strength was needed and although tests were not performed

in this research, USG specifications listed the compressive strength at 10,000 psi for a

0.32 water to gypsum ratio (www.freemansupply.com). An ideal water/gypsum ratio was

determined to be 0.25 for the purposes capping concrete cylinders. Large sheets of glass

were used as a level surface to ensure the end-smoothness requirement standard. An

41

estimated set time of 17 to 20 minutes was beneficial when many cylinders had to be

capped in a minimal amount of time. A picture a hardened gypsum end cap can be seen

in Figure3.1.

Figure 3.1 - Gypsum Cylinder End Cap

3.2 CREEP

Concrete used in floating bridges must be analyzed for its creep potential and

there is need for important experimental investigations into appropriate mix designs for

use in these types of bridges. For this research, creep frames had to first be designed and

fabricated. A basic creep frame schematic pictured in Annual Book of ASTM Standards

was used as a basis for the design. Other frame designs and configurations were

considered, but this one was selected due to its simplicity and its efficiency. ASTM

C512 provides a written description of the basic creep frame design. The standard

42

requires that the frame be capable of applying and maintaining the desired load on the

specimen, despite any changes in the axial length of the specimen. The frame design is

shown in Figure 3.2 and Figure 3.3.

Figure 3.2 - CAD Drawing of Creep Frames

43

Figure 3.3 – Creep Frame

Creep frames must be designed with the strength of the concrete to be tested as

the main parameter and all of the components in the frame including the compression

springs, steel bar diameter and strength, and the plate sizes and strength are sized

accordingly. Concrete mix designs used in recent floating bridge construction has had

ultimate compressive strength values of up to 12,500 psi. An upper limit of 14,000 psi

was selected for the concrete compressive and as the capacity of the creep frames. The

ASTM standard calls for not more than 40% of the maximum compressive strength to be

applied to the concrete cylinders in the creep test. Thus taking 40% of 14,000 psi, a value

44

for the maximum stress that the frame would have to restrain is determined. The stress

value is converted to a force in pounds by multiplying its value by the end surface area of

the six-inch diameter concrete cylinder. This value of approximately 160,000 pounds can

be divided equally among the three rods. The tensile force in each rod is the force that

will be applied to each compression spring

As stated previously, the springs were designed with a strength capacity of 53,000

pounds. For the purpose of the creep test, the springs also had to be designed with a very

high stiffness so that the force would not change considerably due to a minute change in

length. A suitable spring was designed using a high strength steel wire with a diameter of

2.125 in., an outside spring diameter of 9 5/8 in., 12 in. free height, 9 5/16 in. solid

height, spring rate of 22,480 pounds per inch, and total compressed capacity of 60,000

pounds. See Figure 3.4 for a picture of the compression springs.

Figure 3.4 - Creep Frame Compression Springs

45

With the springs designed, the diameter of the steel base plate was sized by

circumscribing three springs in a triangular pattern and this diameter value was

minimized to reduce plate mass and cost. The three threaded, B7 steel reaction rods,

diameter 1.125 inches, were then positioned in a triangular pattern similar to the springs

and moved as close to the center of the plate as the springs and the concrete specimens

would allow. This placement was important to reduce plate deformation, which could

cause unwanted stress concentrations in the concrete. The upper jack plates were sized

according to the bar placements and were minimized to reduce the weight and cost. The

thickness of all of the plates was chosen to be 1.25 inches so that excessive deformation

or yielding would not occur. See Figure 3.5 for plate dimensions. The localized stresses

at the points of threaded rod insertion in the base plate were of particular interest so that

pull out would not occur when the rods were tensioned.

Figure 3.5 - Plate Dimensions

46

To ensure that stress concentrations in the concrete due to slight deviations from

the vertical in load application, a ball and socket joint was fabricated to allow for

specimen rotation. This joint consisted of a high strength steel ball bearing with a

diameter of .625 inches and a steel plate 2 inches thick with a diameter of 6 inches in

order to match the diameter of the specimens. Another plate of equal size, with no

socket, was made and placed on top of the specimens to eliminate stress concentrations

due to the bending of the lower jack plate. In order to ensure an even stress distribution

transfer from the load plates to the concrete specimens the flat surfaces of the end platens

were machined to within the smoothness tolerance listed in ASTM C39 of less than 0.002

inch deviations from plane.

With the design of the creep frame completed, focus was shifted to load

application and load measurement. A 60-ton load jack was sufficient to produce a load

corresponding to the design concrete compressive strength. A hand pump and load jack

system was acquired for the purposes of this test. The hand pump was equipped with a

calibrated dial gage which one could read the applied load to within certain accuracy.

The pump and jack system was calibrated using the Satec Model 400 QC Prism-1007

hydraulic compression machine located in the concrete lab in Albrook Hall. This manner

of load measurement using the dial gage was determined to be a good measure of applied

load. To provide an approximate check of applied load and load loss due to concrete

creep, a strain gage was attached to one of the steel reaction rods in each frame. The

strain gage was connected to a portable strain meter displaying strains in the steel rod,

from which stresses could then be calculated using approximated rod areas and material

47

properties. The tensile stress in the rods was then transferred directly to the axial

compressive stress in the concrete cylinders. Young’s Modulus for the steel rods was

assumed to be 29(10)

3

ksi and was approximately verified using the dial gage on the load

jack. The strain gage placement and orientations can be seen in Figure 3.6.

ASTM C512 calls for concrete cylinders with a diameter of 6 inches and a height

of 12 inches. There are different ways in which strains in the cylinders can be measured,

but only 2 methods are typically practiced. The first method involves an internal strain

gage that is cast within the concrete specimen at the time of batching. A horizontal

concrete mold is used and the gage is positioned in a perfectly longitudinal manner within

the center of the mold. Concrete is then placed and consolidated around the gage. This

method can be accurate, but it is very difficult to position the strain gage and horizontal

Figure 3.6 - Reference Strain Gage

48

molds are less common and more expensive than the typical vertical concrete cylinder

mold.

The second method used for measuring creep and shrinkage strains is the

installment of external gage points on longitudinal planes on the surface of the cylinder

and measuring and recording strains by hand. This method is the one selected to

determine the creep strain in this research. Three planes spaced 120 degrees apart around

the circumference of the cylinder were used so that an average strain could be calculated

for each specimen. A standard gage length of 10 inches is marked on each plane, and 3/8

inch diameter, ½ inch deep holes were drilled using a mill press and a masonry bit. The

drilling process can be seen in Figure 3.7. Brass gage points were glued into these holes

using a strong, waterproof adhesive called JB Weld. With a known initial gage length,

any decrease in length of the cylinders could be measured using a hand-held mechanical

extensometer / compressometer.

Figure 3.7 - Drilling of holes for gage points

49

The mechanical comparator must be accurate to the nearest ten-thousandths of an

inch, which is necessary for the small results expected. A multi position strain gauge was

acquired from ELE International to measure the strain deformations in the creep

specimens. This is a handheld device designed for measuring relative displacement

between the set gage lengths. Due to the length of most creep tests, the device selected

for measuring strain must be durable and stable enough to maintain accurate readings

throughout the length of the tests. The type of strain gage used in this research is

considered stable because it can be calibrated using a constant length standard bar before

every measurement. The gage length of 10 inches mentioned previously was

recommended by Carreira and Burg (Creep and Shrinkage – Structural Design Effects)

and was used in this research. This gage length is the longest span that can be used

without measuring the nonlinear strain regions at the cylinder ends. The mechanical

comparator and creep strain measurement can be seen in Figure 3.8.

Figure 3.8 - Creep strain measurement

50

51

ASTM C512 was used as the basis for the creep test standards. However, some

complications leading up to the testing portion of the experiment lead to some deviations

from the standard. Concrete curing lasted longer than the recommended standard time of

28 days. Due to problems in the preparations for the creep tests, a delay in the start date

was necessary to ensure successful strain measurements. The second phase of concrete

mix batching was done 2 days following the 28

th

day curing for the first phase of

batching, so the delay occurred in both phases of testing. Due to the delays in testing,

curing conditions varied between the two phases of creep tests. The concrete cylinders in

the first phase were cured in a water bath of standard temperature from age 24 hours to

26 days. On the 26

th

day of curing, the cylinders were removed from the water bath and

holes were drilled and gage points were glued in place. End caps were fashioned at this

point as well. The test cylinders were then placed in the controlled environment chamber

in which the creep frames were to be located. The cylinders remained in the chamber

until the 61

st

day of curing on which the creep tests commenced. During the testing

period, the temperature and humidity could not be held constant due to problems with the

chamber control system. The continuous data recorder was out of commission, so only

daily temperature and humidity readings are reported in Table 3.10.

The concrete cylinders in the second phase were cured in a water bath of standard

temperature from age 24 hours to 57 days. At this time, the cylinders were removed from

the water bath and holes were drilled, gage points were glued in place, and end caps were

fashioned. The cylinders were then placed in the controlled environment chamber and

remained unloaded until the 61

st

day of curing, at which the creep tests commenced.

Temperature and humidity data that was recorded for both phases are listed in Table 3.10.

52

The load applied to the concrete cylinders was readjusted periodically throughout

the creep test. This was done in order to maintain a constant stress state in the cylinders.

ASTM C512 requires that the load be adjusted if a change of 2% occurs from the correct

value.

Table 3.10 - Temperature and Humidity History

Phase 1 Phase 2

Test Temperature Humidity

Temperature Humidity

Day (Fahrenheit) (%) (Fahrenheit) (%)

1 73.5 52.0 73.4 54.0

2 73.5 52.0 73.4 54.0

3 76.5 49.0 73.4 54.0

4 82.0 45.0 73.4 54.0

5 73.5 52.0 73.4 54.0

6 67.0 56.0 73.4 54.0

7 - - 73.4 54.0

8 69.3 57.0 - -

9 70.5 59.0 - -

14 77.0 47.0 73.2 52.0

21 71.0 57.0 83.2 48.0

28 72.3 56.0 84.0 44.0

3.3 SHRINKAGE

Two 6x12 inch concrete specimens were cast from each mix design and were to be

used to measure concrete shrinkage. The shrinkage specimens were cured along side

their creep specimen counterparts and were subject to the same environmental conditions

for the duration of the creep test as were listed previously. The specimens remained

unloaded during the creep test. Strains in these specimens were measured in the same

53

manner as that of the creep specimens. Holes were drilled for brass gage points at ten

inch spacing, and strains were measured using the multi position strain gauge from ELE

International.

3.4 COMPRESSIVE STRENGTH

Structural requirements of floating bridges built in recent years have specified a

minimum compressive strength of 6500psi. This was one of the criteria set by a previous

study on concrete for floating bridges and was satisfied and far surpassed in previous

tests of the LVM mix design. It has been documented and noted in the literature review

that the creep potential of concrete is reduced with the increase of compressive strength.

This is a benefit of having concrete with a compressive strength in excess of the design

strength. While maintaining a compressive strength of 6500 psi provides adequate

strength, higher strength concrete can easily be proportioned. The benefits produced in

other performance criteria as a result of this increased strength are almost essential.

The method for testing the compressive strength of concrete was taken from

ASTM C39. For each of the seven mix designs, three 6”x12” replicate cylinders were

made and cured according to ASTM C192. The specimens were immersion cured in a

saturated-lime water bath at 73.4 ± 3°F for 27 days and compressive strength tests were

performed on the 28

th

day of curing. The concrete mixes all had a relatively high design

compressive strength and therefore had to be end-capped for testing, in order to achieve

consistent results, rather than testing with standard neoprene pads and platens. Concrete

cylinders were capped with Hydrostone as described previously. The specimens were

tested for compressive strength using a hydraulic operated machine from SATEC, Model

54

400 QC Prism-1007, Grove City, PA. The longitudinal axis of the specimen was

properly aligned with the thrust of the spherically seated block. A constant rate of

loading was maintained throughout, within the tolerances of the testing machine, and the

rate was within the limits provided in ASTM C39 of 20 to 50 psi per second. Ultimate

compressive stress was recorded, in addition to the type of fracture observed.

3.5 CHLORIDE ION PENETRATION

Durable concrete is defined as having has the ability to withstand external effects,

which may be mechanical, physical, or chemical, with minimal damage. Low

permeability is key to long-term durability of concrete. Low permeability in high

performance concrete provides protection against: damage due to freezing and thawing,

alkali-aggregate reactivity, carbonation, acid attack, chemical resistance, sulfate attack,

seawater exposures, etc. The Hood Canal is an extremely corrosive environment and

care must be taken to ensure that any structural steel within the concrete is protected from

chloride acid attack.

For this test, two 4 by 8 inch cylinders were cast from each mix design. The

cylinders were removed from the molds after 24 hours curing under a plastic tent with

wet burlap. The tent was used to maintain a relatively constant temperature and humidity

of 68 degrees Fahrenheit and 60 %, respectively for the first 24 hours of curing. Upon

removal from the molds, the specimens were partially cured by submersion in lime water

followed by curing in a moisture cabinet until the 28

th

day of curing. The first phase of

three mixes was cured for 22 days in the lime water before the specimens were placed in

the standard cure moisture cabinet. The four mixes in the second phase were water cured

55

for 6 days before the transfer to the moisture cabinet. Tests for Chloride ion penetration

were completed by WSDOT and were performed according to ASTM C 1202.

The experimental methods documented in this chapter are thorough and accurate.

All of the deviations from standard testing methods have been listed and explained.

Further analysis of the effects of these deviations from standard will be included in

upcoming chapters.

56

CHAPTER 4: EXPERIMENTAL RESULTS AND ANALYSIS

The Federal Highway Administration provides classifications for high

performance concrete (HPC) with different performance characteristics. Grades of HPC

are listed from 1 to 4, 1 having the lowest performance in each of the criteria. It should

be noted that HPC grade 1 is still a high performance concrete and performs ”better” than

normal concrete. The information is shown below in its original format in Table 4.1.

Table 4.1 - HPC Performance Grades (Table 1.2 - Definition of HPC according to

Federal Highway Administration, Goodspeed, et al. 1996)

FHWA HPC performance grade

Performance

Characteristics

Standard

test method

1 2 3 4

Freeze-thaw durability

(X = relative dynamic

modulus of elasticity

after 300 cycles)

AASHTO T 161

ASTM

C 666

Procedure A

60%<X<80% 80%<X

Scaling resistance

(X = visual rating of

the surface after

after 50 cycles)

ASTM

C 672

X=4, 5 X=2, 3 X=0, 1

Abrasion resistance

(X = avg. depth of

wear in mm)

ASTM

C 944

2.0>X>1.0 1.0>X>0.5 0.5>X

Chloride penetration

(X = coulombs

AASHTO T 277

ASTM

C 1202

3000>X>2000 2000>X>800 800>X

Strength

(X = compressive

strength)

AASHTO T 2

ASTM

C 39

41<X<55 MPa

(6<X<8 ksi)

55<X<69 MPa

(8<X<10 ksi)

69<X<97 MPa

(10<X<14 ksi)

97 MPa<X

(14 ksi<X)

Elasticity

(X = modulus)

ASTM

C 469

28<X<40 GPa

(4<X<6x10

6

psi)

40<X<50 GPa

(6<X<7.5x10

6

psi)

50 GPa<X<

(7.5x10

6

psi<X)

Shrinkage

(X = microstrain)

ASTM

C 157

800>X>600 600>X>400 400>X

Specific creep

(X = microstrain

per MPa)

ASTM

C 512

75>X>60/MPa

(0.52>X>0.41/psi

60>X>45/MPa

(0.41>X>0.31/psi

45>X>30/MPa

(0.31>X>0.21/psi

30/MPa>X

(0.21/psi>X

57

4.1 CONCRETE MIX DESIGNS

The seven mix designs tested in this research were listed previously in Chapter 3

and can be seen again here in Table 4.2 for reference convenience. All the mix designs

performed well in the batching process. The workability characteristics were comparable.

Superplasticizer was added to each mix at a predetermined quantity, and then adjusted to

achieve the desired slump at or between 8 and 9 inches. There was no indication of

aggregate and cement paste segregation with any of the mix designs. Segregation was

watched for and is an important problem to avoid in floating bridge pontoons due to the

deep walls into which this concrete is to be placed. The freeze thaw characteristic of

concrete is not a major issue in the Hood Canal region, so air content was not measured at

the time of batching.

Table 4.2 - Concrete Mix Design Quantities

M

i



Course Aggregate (lb) 1770 1770 1770 1770 1770 1770 1770

Fine Aggregate (lb) 1295 1295 1295 1295 1295 1295 1295

Portland Cement Type II (lb) 624 540 636.3 597.5 624 624 624

Silica Fume (AASHTO M307) (lb) 50 35 none none 50 50 none

Fly Ash (AASHTO M295) (lb) 100 200 100 100 100 100 100

Metakaolin (Highly Reactive) (lb) none none 38.75 77.5 none none none

Water (lb) 255 255 255 255 258.7 222.12 154.64

Caltite - Waterproofing Admixture none none none none none 49.86 49.86

W/C ratio 0.329 0.329 0.329 0.329 0.334 0.351 0.282

Water Reducer (ASTM C494) none none none none none none none

Superplasticizer (ASTM C494) 5.5 floz/cwt 4.3floz/cwt 5.5floz/cwt 7.0floz/cwt 5.5floz/cwt 5.5floz/cwt 6.3floz/cwt

Slump (inches) 8.0 7.5 9.0 8.5 8.5 8.5 9.0

Caltite -> 6 gallons/yd^3

All Values Based per Cubic Yard

58

4.2 CREEP

Measuring deformations to the precision necessary for accurate creep and

shrinkage results is an intricate task. The accuracy required by ASTM C512 is one ten-

thousandths of an inch. The specimen preparation procedure must be performed with

care. Gage points should be perpendicular with the axis of the cylindrical specimen and

should be parallel with each other so that the mechanical comparator can be used

effectively. Drilling of the holes and gluing the points into the correct position is critical

for useful results. If the gage points are not lined up correctly as previously described,

accurate measurements can still be collected. To collect strain data, the same person

should take all of the measurements and the mechanical comparator must be held at the

same orientation with respect to the specimen and gage points each time a reading is

taken.

Creep potential of concrete is valuable information for knowing if the concrete to

be used in construction is commensurate with the loadings to be applied throughout the

design life of a structure. As was described in detail in the Chapter 1, creep is present in

floating bridge pontoons and must be accounted for. Although creep deformation will

continue throughout the life of a structure, it is essential that predictions of long term

creep could be made based on short term data. Typically, creep tests are carried out for

180 days or up to one year or more. The expected creep strain after this time is much less

than that which would occur during the testing duration. As was stated in the literature,

(Brooks and Neville 1978) required creep accuracies for a given concrete application

should be assessed so that appropriate test duration could be selected. Short term, 28 day

tests were selected for this research. Such data can be used to observe concrete creep

59

5.0

28

)05.12)(log61.3(100 −+= tss

et

potential at 28 days, and to extrapolate long-term results using empirical relationships.

The extrapolation equations and expected error developed by Brooks and Neville (1978)

are provided here in a revised form:

Basic creep- c

t

=c

28

*0.50t

0.21

; M

bc

≈16%

Total creep- c

t

=c

28

[-6.19+2.15ln(t)]

1/2.64

; M

tc

≈19%

Shrinkage-

M

sh

≈14%

Measured and calculated creep quantities are shown in Table 4.3. The table lists

for each mix number, the applied stress, the instantaneous elastic deformation, the

calculated Young’s Modulus, measured 28-day creep, the 28-day creep coefficient, 28-

day specific creep, and long-term estimated creep strains. A graphical depiction for

comparison of the 28-day measured specific creep values and the long-term extrapolated

values, less the initial elastic strain, is shown in Figure 4.1. Other graphs displaying the

measured deformation of each mix design can be seen in Figures 4.2 through 4.8. For

visual clarity, actual measured data points are included in the graphs, and trend lines have

been sketched over the points to model the data curves. The results are graphed in micro-

strain versus time in days. The total strain was measured from the specimens under load

in the creep frames. Shrinkage strains were measured from the companion cylinders

cured at the same conditions as the creep specimens. The values for creep plus initial

elastic strain have been calculated by subtracting the shrinkage strains from the total

60

strain measured. Initial elastic deformation is included in “creep strain” curves in the

individual mix deformation graphs.

Table 4.3 - Creep Comparison

The axial stress applied to the specimens was approximately 25 % of the

28-day ultimate compressive strength. The dial gage accuracy for the applied

load reading was reported by the

manufacturer to be ±1% of the maximum

number on the gage ring scale. For this particular application, the accuracy is

equal to ±1% of 65 tons, or .65 tons.

The instantaneous elastic deformation is is the measured strain immediatly after

the load is applied to the specimens. This strain is almost entirely recoverable when the

load is removed. This portion of the total load induced strain is not considered creep and

therefore, not included in the reported creep strain results. This property was described

by Neville, Dilger and Brooks (1983). The modulus of elasticity of the concrete is

calculated by dividing the applied stress by the instantaneous elastic strain. This Young’s

modulus is the initial value for the hardened concrete. As the concrete undergoes long

term deformation under applied load, the modulus of elasticity is reduced. The values

reported here in Table 4.3 are comparable to values seen in other research. In a study

performed by Cascade Testing in Seattle, a MOE for a mix similar in composition to the

LVM mix design was reported as 6.27(x10

6

) psi. This is the same as the valued

M

i

x

#

I

n

s

t

a

n

1

.

3

2

.

2

3

.

2

4

.

3

5

.

3

6

.

2

7

.

2

64.2

1

))(log*15.219.6(

28

t

e

c

t

+−=

61

calculated for mix design #5. The MOE reported for a mix similar in composition to the

Caltite mix design was reported as 6.77(x10

6

) psi, indicating a 1% difference from the

value calculated in this research of 6.84(x10

6

) psi.

The 28-day creep is the actual measured strain for each concrete mix. The

deflection was measured in inches for each gage length on both specimens for a given

mix design. Each deflection measurement was divided by its respective gage length in

inches to obtain a strain value. These strain values were then averaged for each mix

design to obtain the value listed in Table 4.3. A routine check of strain similarity

between creep cylinders can be made by observing the measured data. For mix #1,

average total strain for cylinder 1 was recorded as 0.00088 in/in, and the average total

strain for cylinder 2 was 0.00088 in/in. This produced an average of 0.00088 in/in with a

standard deviation of 0.0. The standard deviation for the measured total strain data for

mix 3 is 0.000014.

The results The 28-day creep coefficient is the ratio between the measured creep

value at 28 days and the instantaneous elastic strain. It is important to note that creep

strains are relative, based on the stress applied to the specimens. A constant ratio

between applied and ultimate compressive stress has been used in this research.

Normalization to comparable data is done by dividing the strain in the cylinders by the

stress applied, resulting in the specific creep values presented in the Table 4.3. Specific

creep is reported in units of microstrain per psi and is used when comparing creep

potential of different mix designs. Extrapolated specific creep values for times of 180

days, 1 year and 5 years are also reported and listed in Table 4.3. The long term data was

62

0.000

0.100

0.200

0.300

0.400

0.500

0.600

0.0 500.0 1000.0 1500.0 2000.0

Time (days)

Specific Creep (microstrain/psi)

Mix #1 Mix #2

Mix #3 Mix #4

Mix #5 Mix #6

Mix #7

calculated using the 28 day specific creep data and the equation previously reported from

Brooks and Neville (1978).

Figure 4.1 – Specific Creep Comparison – Estimated Strain Results to 5-Years

63

Dilger and Wang (2000) made the observation that creep strains for a high

performance concrete mix are approximately 1.8 to 2.4 times the initial instantaneous

elastic strain after a long time. This principle is fairly consistent with the mixes tested in

this research. For one year extrapolated data, the creep coefficient ranges from 2.16 for

mix #6 to 2.67 for mix #4.

Mix #2 had the lowest measured value for specific creep. A value of 0.128

micro-strain at 28 days was 22% lower than Mix #3, which had the next lowest specific

creep results. It has been noted that mix #2 had the highest quantity of fly ash of all the

mixes tested. Brooks (1999) found that fly ash was shown to result in lower ultimate

creep values with an increase in cement replacement percentage of fly ash. This is

because fly ash concrete continues to develop strength over a long period, unlike silica

fume, which leads to faster development of ultimate compressive strength. Brooks

(2000) also found that total creep decreases for low levels of silica fume. Both the higher

level of fly ash and the lower level of silica fume in mix #2 helped produce the concrete

with the lowest creep potential researched in this study.

Mix #7 had low specific creep, with a 28-day value of 0.165 micro-strain. This

could be attributed to the relatively low water-to-cementitious ratio of 0.28 (Burg et.al.

1994). This particular mix had low cement paste content with respect to the other

concretes. A decrease in cement paste content tends to produce concrete with decreased

creep (Zia, 1993). Furthermore, high aggregate content is known to restrain creep

deformations. It is unknown whether the Caltite lead to the reduction in creep as

compared to the baseline mix. Referring to mix #6, the Caltite inclusion into the concrete

64

did not appear to considerably affect creep of the LVM mix. Similar values for creep

were obtained for mix #6 as were for the LVM.

The LVM mix designs, #’s 1 and 5, produced creep values of slightly differing

magnitude. Both extrapolated creep values at 180 days are classified as Grade 2

according to Figure 4.1. The values are resulting from concretes with different curing

conditions and from a test that is difficult to repeat and achieve duplicate results.

Metakaolin modified concrete was similar to silica fume modified concrete in its

creep potential. Mix #4 creep deformation, 0.340 micro-strain, was nearly equivalent to

the creep of its counterpart, the LVM number 2, at 0.336 micro-strain at 180 days. Mix

#3 performed better in creep than did mix #4. This was not expected since results

observed in the literature claimed that creep of metakaolin modified concrete decreased

with the increased inclusion quantity of metakaolin in the mix (Brooks et.al. 2001). The

effect of the curing conditions may have affected the creep potential of the concrete. The

loss of internal relative humidity from cement hydration as well as water loss to the

ambient environment as the concrete cured in the testing chamber could have led to lower

total creep in mix #3, compared to that of mix #4 (Dilger et.al 2000).

65

y = 9.5728Ln(x) + 37.163

y = 61.879Ln(x) + 582.92

y = 71.452Ln(x) + 620.08

0

100

200

300

400

500

600

700

800

900

1000

0.0 5.0 10.0 15.0 20.0 25.0 30.0

Time (days)

Strain (in/in) (10^-6)

Total Strain

Creep and Initial Elastic Strain

Shrinkage Strain

Figure 4.2 - LVM Mix Design Strain

y = 29.073Ln(x) + 198.14

y = 28.373Ln(x) + 352.98

y = 57.445Ln(x) + 551.12

0

100

200

300

400

500

600

700

800

900

1000

0.0 5.0 10.0 15.0 20.0 25.0 30.0

Time (days)

Strain (in/in) (10^-6)

Total Strain

Creep and Initial Elastic Strain

Shrinkage Strain

Figure 4.3 – WJE Inc. Mix Design Strain

66

y = 17.905Ln(x) + 67.883

y = 43.29Ln(x) + 434.8

y = 61.195Ln(x) + 502.68

0

100

200

300

400

500

600

700

800

900

1000

0.0 5.0 10.0 15.0 20.0 25.0 30.0

Time (days)

Strain (in/in) (10^-6)

Total Strain

Creep and Initial Elastic Strain

Shrinkage Strain

Figure 4.4 – 5% Metakaolin Mix Design Strain

y = 9.946Ln(x) + 51.429

y = 58.024Ln(x) + 560.96

y = 48.078Ln(x) + 509.54

0

100

200

300

400

500

600

700

800

900

1000

0.0 5.0 10.0 15.0 20.0 25.0 30.0

Time (days)

Strain (in/in) (10^-6)

Total Strain

Creep and Initial Elastic Strain

Shrinkage Strain

Figure 4.5 – 10% Metakaolin Mix Design Strain

67

y = 7.1314Ln(x) + 36.302

y = 42.682Ln(x) + 512.51

y = 49.814Ln(x) + 548.82

0.0

100.0

200.0

300.0

400.0

500.0

600.0

700.0

800.0

900.0

1000.0

0.0 5.0 10.0 15.0 20.0 25.0 30.0

Time (days)

Strain (in/in) (10^-6)

Total Strain

Creep and Initial Elastic Strain

Shrinkage Strain

Figure 4.6 – LVM (#2) Mix Design Strain

y = 12.169Ln(x) + 52.182

y = 33.95Ln(x) + 421.69

y = 45.193Ln(x) + 474.95

0

100

200

300

400

500

600

700

800

900

1000

0.0 5.0 10.0 15.0 20.0 25.0 30.0

Time (days)

Strain (in/in) (10^-6)

Total Strain

Creep and Initial Elastic Strain

Shrinkage Strain

Figure 4.7 – LVM Mix w/ Caltite Waterproofing Admixture Mix Design Strain

68

y = 10.959Ln(x) + 48.823

y = 27.743Ln(x) + 332.03

y = 38.702Ln(x) + 380.86

0

100

200

300

400

500

600

700

800

900

1000

0.0 5.0 10.0 15.0 20.0 25.0 30.0

Time (days)

Strain (in/in) (10^-6)

Total Strain

Creep and Initial Elastic Strain

Shrinkage Strain

Figure 4.8 – Caltite Mix Design Strain

69

4.3 SHRINKAGE

The engineers that designed the Lacey V. Murrow Bridge specifications placed a

limit on the maximum allowable shrinkage strains in the pontoons. The length change of

hardened concrete, tested according to AASHTO T160 or ASTM C 157, was required to

be less than 400 millionths (micro-strain) at 28 days. As was discussed previously,

shrinkage strain must be kept to a minimum so that shrinkage cracking does not occur

and allow water to penetrate into the pontoon cells.

The shrinkage testing method provided by ASTM C 157 was not used in this

research. Obtaining shrinkage strains in a similar manor as the strains due to creep was

desirable for direct comparisons and calculations. This method is prescribed by ASTM C

512 where necessary information requirements for creep are specified. It should be noted

that due to the creep testing procedure described previously, measurements for shrinkage

strains were not taken until the time the creep cylinders were subject to loading. This

being the case, actual data reported for shrinkage are not true 28-day values. The curing

conditions prior to strain measurements and age at testing have been described and

should be noted when reviewing the shrinkage results. The 28-day measured shrinkage

strain can be seen in Table 4.4.

Values observed for shrinkage strain are all classified as Grade 3 concrete strains

according to FWHA, with mix #2 as the one exception, which is classified as

Performance Grade 2. All mixes had shrinkage results well below the required limit of

400 millionths at 28 days. The LVM mix design, both numbers 1 and 5, performed quite

well and had the lowest shrinkage strains observed here. As was expected, mixes

containing silica fume experienced slightly lower shrinkage than the mixes containing

70

similar quantities of metakaolin, at early ages. (Calderone, Gruber, Burg 1994) This was

observed in the comparison of the LVM to mix #4. In addition, shrinkage strains showed

a decrease as the OPC replacement quantity by metakaolin increased (Ding, Li 2002).

Caltite did not significantly affect shrinkage of the LVM mix, however a slight increase

was observed.

With the exception of mix #2, all mix designs performed as expected in

shrinkage. Mix design #2 had the highest shrinkage strain measured in this research.

This occurrence is possibly because more water still existed in the concrete cylinders.

The higher water content is due to the continuing of hydration over a longer period

because of the high fly ash content. More water in the concrete would allow for more

drying shrinkage as the concrete attempts to reach hygral equilibrium with the ambient

environment. These results, however, are larger than expected when considering the

curing conditions that the test specimens experienced prior to strain measurements.

71

Table 4.4 – Shrinkage Strains

Mix #

Modulus of

Elasticity

(10^6)

(s/e

i

) psi

28 Day

Shrinkage

(microstrain)

(s

28

)

Estimated

Long Term

Shrinkage

(microstrain)

c

t

=180 days

Estimated

Long Term

Shrinkage

(microstrain)

c

t

=365 days

Estimated

Long Term

Shrinkage

(microstrain)

c

t

=1825 days

1

6.76 96.7 355.5 400.8 484.8

2

8.41 289.5 548.3 593.6 677.5

3

7.30 135.0 393.7 439.1 523.0

4

7.01 121.8 380.6 425.9 509.8

5

6.27 83.4 342.2 387.5 471.4

6

5.69 116.7 375.5 420.9 504.8

7

6.84 128.6 387.3 432.7 516.6

Figure 4.9 – Long Term Shrinkage Strains, Extrapolated from 28-day Data

5.0

28

)05.12)(log61.3(100 −+= tss

et

Long Term Shrinkage Strains

0.0

100.0

200.0

300.0

400.0

500.0

600.0

700.0

800.0

0 200 400 600 800 1000 1200 1400 1600 1800 2000

Time (days)

Shrinkage - 10^-6

Mix #1 Mix #2

Mix #3 Mix #4

Mix #5 Mix #6

Mix #7

72

4.4 COMPRESSIVE STRENGTH

The results for 28-day compressive strength can be seen in Table 4.5. The testing

protocol followed to obtain strength data is prescribed by ASTM C39, as listed in Section

3.4 of this report. Three cylinders were cast and cured for each mix design and tested in

axial compression on the 28

th

day. Standard deviations for the mean compressive

strength are listed in Table 4.5 and are all within the requirement of 7.8% set forth in

ASTM C39.

Mix design 4 produced the highest compressive strength with an average ultimate

value of 9206.7 psi. The LVM mix design, numbers 1 and 5 with an average of the two

average ultimate values of 8788.4 psi was the next highest value obtained in this research.

The results of these two mixes are consistent with previous research findings mentioned

in the literature review chapter of this report. Concrete compressive strength is greater

with the inclusion of metakaolin than that of concrete with silica fume with similar OPC

replacement values. The results of mix numbers 2 and 3 are also consistent with past

metakaolin and silica fume comparison studies. Mix number 2 was proportioned with

4.5% OPC replacement with silica fume and mix number 3 had 5% OPC replacement

with metakaolin. Mix number 3 demonstrated a higher ultimate compressive strength

than number 2 by 7.5%.

The first mix incorporating Caltite, mix number 6, had a compressive strength of

6890 psi, which was lower than its parent mix design, the LVM, with an average

compressive strength of 8788 psi. These results were consistent with past results from a

similar study by Cascade Testing in Seattle, Washington where a control mix and a

similar mix having water replaced by equal part Caltite were tested. The 28-day

73

compressive strength of the control mix was 12310 psi and that of the Caltite mix was

9980 psi. The reduction in compressive strength seen in this previous study of about 19.0

percent is similar to the results of this research of 21.6 percent. The Caltite was used as a

water replacement and accounted for as water in the water-to-cementitious material ratio.

The water-to-cementitious ratio was larger for this mix than the other mix designs tested

in this study. This larger ratio may have been the cause for the lower strength, as past

results have shown (Carette and Malhotra,1992). In addition, Caltite may not contribute

to the hydration process in the same manor as water does. Due to the removal of water

and replacement with Caltite, it could be speculated that similar hydration may not have

been possible, which could produce concrete with reduced strength.

Mix design 7 had a 28-day compressive strength of 6233.3 psi. As previous

results demonstrated, greater compressive strengths result from the inclusion of finer

supplementary cementitious materials such as silica fume or metakaolin (Calderone,

Gruber, Burg, 1994). The lower strength was expected due to the lack of these fines in

the mix design. Mix number 7 had the lowest strength of all of the mix designs tested,

and was just slightly lower than the required compressive strength of 6500 psi set forth in

the concrete specifications.

74

Table 4.5 – 28-Day Compressive Strength

28 day

Average

28- Day

Cylinder

Compressive Standard Compressive

Mix Design

# Strength (psi) Deviation Strength (psi)

1 8910

1 2 8650 177.8 8710

3 8570

1 8140

2 2 8200 32.1 8163.3

3 8150

1 8820

3 2 8780 50.3 8773.3

3 8720

1 9340

4 2 9080 130.1 9206.7

3 9200

1 8870

5 2 8820 45.1 8866.7

3 8910

1 7010

6 2 6800 108.2 6890

3 6860

1 6100

7 2 6350 125.8 6233.3

3 6250

0

1000

2000

3000

4000

5000

6000

7000

8000

9000

10000

Mix Design

Compressive Strength (psi)

#1 #2 #3 #4 #5 #6 #7

Figure 4.10 – 28-Day Compressive Strength

75

4.5 CHLORIDE ION PENETRATION

ASTM C 1202 prescribes the testing method for determining the chloride

penetration resistance in of the concrete mixes. Two 4 by 8 standard cylinders were cast

for each mix to execute this test, as was stated in Section 3.5. Test results for the 28-day

cure chloride ion penetration tests can be seen in Table 4.6.

First, it should be noted that based on the creation of the LVM mix design, a

chloride permeability resistance adequacy standard was set at a maximum of 1000

coulombs passed at 56 day cure. Results for 56-day cure chloride permeability were not

determined in this research due to lack of test cylinders. This is a slight drawback since

the results cannot be compared directly to the permeability requirement set forth as a

basis for acceptability. However, trends can be noted using the 28-day data and the

results can be compared with those from prior studies to determine the adequacy of

chloride ion penetration resistance.

The lowest penetration result was mix number 5, the second phase LVM mix

design. The low level of charge passed, 1158 coulombs, was consistent with previous

LVM mix design permeability results. Lwin, Bruesch, and Evans (2001) reported test

results from initial LVM mix design development studies. Permeability results reported

were 1,198 coulombs at 28 days. This value was reduced to 790 coulombs at 56 days and

then further reduced to 584 coulombs at 90 days. At the time of the LVM construction,

113 permeability tests were performed on the LVM concrete and the results were

reported in the Concrete for Lacey V. Murrow Bridge Pontoons (1993), a WSDOT

document. The results for 28, 56 and 90-day tests had averages of 1327, 785, and 577

coulombs, respectively. The decrease in permeability is due to the further hydration of

76

the concrete with time and the resulting infilling of the porosity. This typical

characteristic of concrete can be assumed to act in a similar manor for all of the mixes

studied in this research. Thus, it can be assumed that all of the permeability values would

decrease as the cure time increased. Boddy, Hooton and Gruber (2001) demonstrated

such property in a study in which long-term chloride penetration resistance of concrete

containing high reactivity metakaolin was explored.

The addition of Caltite to the LVM mix to form mix design #6 increased the

chloride penetration at 28 days to 1337 coulombs. This amounted to a 15% increase in

permeability, though this mix design was the second most resistant to chloride ion

penetration in this research.

Mix design number 4, the metakaolin mix with 10% OPC replacement had

chloride permeability of 1682.5 coulombs. According to past studies, metakaolin

concrete has a similar, but slightly lower resistance to chloride ion penetration than does

silica fume concrete during early stages. Ding and Li (2002) found that for all OPC

replacement values, silica fume is more effective in providing improved chloride

resistance of concrete than metakaolin, but both were considerably better than their

control mix with no fine supplementary cementitious materials. Ding and Li reported

though, that after 90 days of observation, the silica fume and metakaolin 15%

replacement concretes displayed equal resistance results. This is a testament to the nearly

100% reactivity of the metakaolin and the further hydration that results over time. Due to

the results trend reported by Ding and Li, as well as conclusions reached by Boddy,

Hooton and Gruber (2001), it could be speculated that the permeability of the 10%

77

metakaolin modified concrete would reduce to below 1000 coulombs at 56 days, and

further reduction would occur by 90 days.

The conclusions to the aforementioned study by Ding and Li were not repeated

here when comparing mix number 2, the WJE Inc. mix recommendation containing 5%

silica fume, to mix number 3, which contained 5% metakaolin as OPC replacement. Mix

numbers 2 and 3 had chloride resistance results of 2380 and 1938.5 coulombs,

respectively. At 28 days, the metakaolin modified concrete showed greater resistance to

chloride penetration than did the fly ash and silica fume concrete. It should be noted that

the water to cementitious ratio was the same for both mixes, but the fly ash quantities

differed greatly between the two. Due to its reaction with OPC hydration and its small

size compared to OPC, it was shown that fly ash typically decreases concrete

permeability (Aitcin 1998), but this has not been displayed here in this early age test.

The curing conditions for these two mixes, as described in the Experimental Methods

chapter of this report, were alike, so the metakaolin mix simply outperformed the WJE

Inc mix in resistance to chloride ion penetration. It should be assumed that the

permeability of these mixes would decrease drastically by the 56

th

day of curing, possibly

reducing the amount of coulombs passed by half. In a previous study (Ozyildirim,1998)

examining the permeability of a concrete mix similar in proportion to mix 2, the number

of coulombs passed reduced from 1454 at 28 days to 490 at 90 days.

Mix design number 7 had the largest chloride ion penetration at 2858 coulombs

at 28 days. This is classified by ASTM C1202 as moderate. Due to the lack of a fine

supplementary cementitious material, such as silica fume or metakaolin, the porosity of

this mix was greater than the other mixes. It should be noted that a previous 58-day

78

chloride ion permeability test on a mix similar in composition to mix 7 produced an

average result of 895 coulombs (CTL 1999)

Table 4.6 – Rapid Chloride Permeability Test Results - 28 day

28 – Day

Charge Passed Average Chloride Ion

Mix Design Cylinder # (Coulombs) Coulombs Penetrability

8 1598

1

9 1660

1629* Low

17 2340

2

18 2420

2380 Moderate

26 1917

3

27 1960

1938.5 Low

35 1648

4

36 1717

1682.5 Low

44 1183

5

45 1133

1158* Low

53 1340

6

54 1334

1337 Low

62 2916

7

63 2800

2858 Moderate

Table 4.7 – Permeability Classifications

Chloride Ion Penetrability Based on Charge Passed

Charge Passed (coulombs)

Chloride Ion Penetrability

>4,000 High

2,000-4,000 Moderate

1,000-2,000 Low

100-1,000 Very Low

<100

Negligible

(ASTM C 1202 – 97)

79

80

CHAPTER 5: SUMMARY AND CONCLUSIONS

This research provides a comparative study of several concrete mix designs for

use in floating bridges for the purpose of improvements in existing practices. The Lacey

V. Murrow (LVM) mix design is used as a baseline mix and alterations are made to that

design to improved the concrete performance.

The concrete mixes were studied for their fresh and hardened properties including

the 28-day compressive strength, chloride ion permeability, creep and shrinkage. For

purposes of comparison and determination of a better mix design, it is advantageous to

have a reference mix. Results are tabulated in Table 5.1 and should be referred to when

reviewing the conclusions reached.

Results of this research reiterates that the LVM mix design is a quality, high

performance concrete mix. The LVM has performed well in all the categories tested, and

has only slightly been improved in some areas by certain mix alterations. Though the

mix design was developed in 1991, it remains a mix that is quite suitable for use in

concrete floating bridges. Bridge designers must evaluate the importance of minor

improvements in the LVM concrete performance for the benefits in the application.

Table 5.1 – Mix Design Test Results

Predicted Predicted

Average 28 day

Chloride 180-Day 180-Day

Compressive Average Ion Specific Creep Shrinkage

Mix Design

Strength (psi) Coulombs

Penetrability

(microstrain/psi) (microstrain)

Baseline 8788 1394 Low 0.359 349

2 8163 2380 Moderate 0.236 548

3 8773 1939 Low 0.297 394

4 9207 1683 Low 0.340 381

6 6890 1337 Low 0.343 376

7 6233 2858 Moderate 0.303 387

81

Mix design number 2 is a modified LVM mix, with decreased silica fume and

increased fly ash contents. The workability was acceptable and the fresh concrete could

attain similar slump to the LVM of 7.5 inches with a lesser amount of superplasticizer.

There was no indication of segregation. The 28-day compressive strength was 7.1%

lower, the permeability was classified as moderate, the 180-day specific creep decreased

by 34.3%, and the 180-day shrinkage was 57.2% greater than the baseline mix.

Mix design number 3 consists of high reactivity metakaolin at 5% OPC

replacement. Fly ash content was the same as the LVM and no silica fume was included.

The fresh concrete showed excellent performance with a slump of 9 inches when using an

equal amount of superplasticizer as the LVM mix. Compressive strength was only

slightly less by 1.7%, permeability was low, creep was reduced by 17.3%, and shrinkage

increased by 12.9%.

Mix design number 4 contains 10% high reactivity metakaolin as a supplementary

cementitious material. Fly ash content was the same as the LVM and no silica fume was

used. An 8.5-inch slump was measured with 7.0 fluid oz/cwt. The compressive strength

showed an increase over the LVM by 4.8%, permeability was low, 180-day specific creep

was reduced by 5.3%, and shrinkage increased by 9.1%.

Mix design number 6 contains the same quantities of cementitious materials and

superplasticizer as the baseline design, with a portion of the water replaced by Everdure

Caltite waterproofing admixture. Workability was excellent with the fresh concrete

attaining a slump of 8.5 inches. The compressive strength was decreased by 21.6%,

chloride ion permeability was low, creep was lower by 4.5%, and shrinkage was greater

than the LVM by 7.7%.

82

Mix design number 7 contains similar aggregate quantities as the LVM, as well as

equivalent amounts of OPC and fly ash. Silica fume is not used in this mix. Everdure

Caltite is added in place of equal parts mix water. The concrete attained a slump of 9.0

inches using 6.3 fluid oz/cwt of superplasticizer. The 28-day compressive strength was

6233.3 psi, showing a reduction in strength of 29.1%. The chloride ion permeability was

moderate, 180-day specific creep was 15.6% lower than the baseline mix, and shrinkage

increased by 11.0%.

General conclusions from the results of this research have been realized. The

reduction of silica fume and increase of fly ash proved successful in attaining required

specification properties. LVM concrete properties were improved by the inclusion of

high-reactivity metakaolin in some cases. Caltite waterproofing admixture reduced

chloride ion permeability in the LVM mix, but decreased 28-day compressive strength.

Concrete with insufficient compressive strength was created with the removal of silica

fume and the inclusion of Caltite.

The results and conclusions reached are reliable and can serve a valuable tool in

the selection of concrete for use in floating bridges. As is the case with any concrete mix,

tests must be performed to ensure the suitability for a given application. This research

could be viewed as a first step in the selection and testing of a concrete mix. However,

prior to implementing a particular mix, an engineer may need to perform additional tests

to ensure compliance with desired performance criteria. Large-scale wall and slab

sections representative of the bridge pontoons in which the concrete is to be used should

also be tested to ensure satisfactory constructability performance. Such studies are

critical for the successful implementation of a given concrete mix in floating bridges.

83

REFERENCES

1. “Concrete for Lacey V. Murrow Bridge Pontoons,” (1993). Wiss, Janney, Elstner

Associates, Inc. WJE No. 912145

2. “Results of ASTM C666 Rapid Freezing and Thawing, AASHTO T277 Rapid

Chloride Permeability, and AASHTO T259/260 90 Day Chloride Solution

Ponding of Specimens From Nine Concrete Mixes,” (1999). Construction

Technology Laboratory, Skokie, Illinois

3. Aitcin, P.C. (1998). High Performance Concrete. London. E & FN Spon.

4. Brooks, J. J. (2000). “Elasticity, Creep and Shrinkage of Concretes Containing

Admixtures,” ACI Special Publication 194, pp283-360

5. Brooks, J. J. (1999). “How Admixtures Affect Shrinkage and Creep,” Concrete

International, April

6. Brooks, J. J. and Johari, M.A. Megat. (2001). “The Affect of Metakaolin on

Creep and Shrinkage of Concrete,” Cement and Concrete Research

7. Brooks, J. J. and Neville, A. (1992). “Creep and Shrinkage of Concrete As

Affected by Admixtures and Cement Replacement Materials,” ACI Special

Publication 135-2, pp19-36

8. Brooks, J. J. and Neville, A.M. (1975). “Estimating Long-term Creep and

Shrinkage from Short-term Tests,” Magazine of Concrete Research. Vol 27 No.

90; March, pp. 3-12

9. Brooks, J. J. and Neville, A.M. (1978). “Estimating Long-term Creep and

Shrinkage from Short-term Tests,” Magazine of Concrete Research. Vol 30 No.

103; pp. 51-61

10. Burg, R.G. and Ost, B.W. (1994). “Engineering Properties of Commercially

Available High Strength Concretes,” Research and Development Bulletin - RD

104, Portland Cement Association, Skokie, Illinois, USA

11. Calderone, M. A., Gruber, K. A., and Burg, R. G. (1994). “High Reactivity

Metakaolin: A New Generation Admixture,” Concrete International, Nov, pp 37-

40

12. Carreira, D.J. and Burg, R.G. (2000). “Testing for Concrete Creep and

Shrinkage,” ACI Special Publication 194, pp381-420

84

13. Carrette, G.G., Bilodeah, A., Chevrier, R.L., and Malhotra, V.M. (1993).

“Mechanical Properties of Concrete Incorporating High Volumes of Fly Ash from

Sources in the U.S.,” ACI Materials Journal, Nov-Dec, Vol. 90 No.6, pp.535-544

14. Carrette, G.G.and Malhotra, V.M. (1992). “Long-Term Strength Development of

Silica Fume Concrete”, Proceedings, Canmet/ACI 4

th

International Conference

on Fly Ash, Silica Fume, Slag and Natural Pozzolans in Concrete, Istanbul, ACI

SP-132, vol. 2, ed. V.M. Malhotra, American Concrete Institute, Farmington

Hills, Mich., pp. 1651-1671

15. Collins, T.M. (1989). “Proportioning High-Strength Concrete to Control Creep

and Shrinkage,” ACI Materials Journal, Nov-Dec, Vol 86, No. 6, pp.576-580

16. Dhir, R. K. and Dyer, T. D. (1999). Modern Concrete Materials. Thomas

Telford Publishing, London

17. Dilger, W.H. and Wang, C. (2000). “Creep and Shrinkage of High Performance

Concrete,” ACI Special Publication 194. pp 361-371

18. Ding, J.T. and Li, Z. (2002). “Effects of Metakaolin and Silica Fume on

Properties of Concrete,” ACI Materials Journal V. 99, No. 4, July-August. pp

393-398

19. Dusenberry, D. O. (1993). “What Sank the Lacey Murrow?,” Civil Engineering

(New York), v. 63, n. 11, Nov. p 54-57.

20. Feng, N.Q., Chan, S.Y.N., He, Z.S. and Tsang, M.K.C. (1997). “Shale Ash

Concrete,” Cement and Concrete Research, Vol. 27 No. 2, pp. 279-291

21. Firth, C. R. (1993). “What Sank the Lacey Murrow? The Contractor’s Case,”

Civil Engineering (New York), v. 63, n. 11, Nov. p 58-59.

22. Gloyd, Charles S., (1988) “Concrete Floating Bridges,” Concrete International,

May

23. Goodspeed, C. H., Vanikar, S. and Cook, R. A. (1996). Concrete International,

Vol 18, Issue 2, February

24. Jianyong, Li and Yan, Y. (2001). “A Study on Creep and Drying Shrinkage of

HPC,” Cement and Concrete Research 31, pp 1203-1206

25. Khatri, R. P. (1995). “Effect of Different Supplementary Cementitious Materials

on Mechanical Properties of HPC,” Cement and Concrete Research, Vol. 25, No.

1

85

26. Lwin, M. Myint (1999). Chapter 22 - Floating Bridges. Bridge Engineering

Handbook, CRC Press, LLC

27. Lwin, M. Myint, (1989). “Design of the Third Lake Washington Floating Bridge,”

Concrete International, Feb. p 50-53.

28. Lwin, M. Myint, Bruesch, Alan W. and Evans, Charles F. (2001). “High

Performance Concrete for a Floating Bridge,” Fourth International Bridge

Engineering Conference; pp. 155-162

29. Lwin, M. Myint, Gloyd, Charles S. (1984). “Rebuilding the Hood Canal Floating

Bridge,” Concrete International, June, p 30-35.

30. Lwin, M. Myint. (1993). “Floating Bridges – Solution to a Difficult Terrain,”

Transportation Facilities through Difficult Terrain, Wu & Barrett. Balkema,

Rotterdam, ISBN 90 5410 3434

31. Memon, A.H., Radin, S.S., Zain,M.F.M. and Trothier, Jean-Francois. (2002).

“Effects of Mineral and Chemical Admixtures on High Strength Concrete in

Seawater,” Cement and Concrete Research 32, pp 373-377

32. Neville, A.M., Dilger, W.H. and Brooks, J.J. (1983). Creep of Plain and

Structural Concrete, Longman Inc; New York.

33. Nichols, C. C., (1964). “Construction and Performance of Hood Canal Floating

Bridge,” Symposium of Concrete Construction in Aqueous Environments. ACI

Publication SP-8, P. 97-106. ACI

34. Ozyildirim, C. (1998). “Fabricating and Testing Low-Permeability Concrete for

Transportation Structures,” VTRC 99-R6, Virginia Transportation Research

Council, FHA, August

35. Paulson, K.A., Nilson, A.H., Hover, K.C. (1991). “Long-Term Deflection of

High-Strength Concrete Beams,” ACI Materials Journal, Mar-Apr, Vol 88, No. 2,

pp. 197-206

36. Persson, Bertil. (2001). “A Comparison between Mechanical Properties of Self-

Compacting Concrete and the Corresponding Properties of Normal Concrete,”

Cement and Concrete Research 31, p 193-198, USA

37. Ramachandran, V.S. (1995). Concrete Admixtures Handbook, 2

nd

Edition; Noyes

Publications; Park Ridge, New Jersey, USA

38. Sicker, A. and Huhn, M. (1997). “The Influence of Admixtures on the

Rheological Properties of Mortars,” Helm Lacer No. 2

86

39. Xu, Yunsheng and Chung, D. D. L. (2000). “Improving Silica Fume Cement by

Using Silane,” Cement and Concrete Research

40. Yamamoto, T. (1990). “Creep and Shrinkage of High-Strength Reinforced

Concrete Columns,” Transactions of the Japan Concrete Institute, Vol. 12, pp.

101-106

41. Zia, P., Ahmad, S.H., Leming, M.L., Schemmel, J.J. and Elliott, R.P. (1993).

“Mechanical Behavior of High Performance Concretes, Volume 5: Very High

Strength Concrete,” Strategic Highway Research Program, National Research

Council, Washington, D.C., xi, 101pp. (SHRP-C-365)

42. Zia, P., Leming, M.L., Ahmad, S.H., Schemmel, J.J., Elliott, R.P., and Naaman,

A.E. (1993). “Mechanical Behavior of High Performance Concretes, Volume 1:

Summary Report.” Strategic Highway Resesarch Program, National Research

Council, Washington, D.C., xi 98, pp. SHRP-C-361.

87

CHAPTER 6: LITERATURE REVIEW

This literature review focuses on three main topics. The first one is the history of

floating bridges with special attention to the Hood Canal Floating Bridge. The second

topic is on mix designs used on past floating bridges in the state of Washington. Finally,

the third topic is on concrete experiments that addressed leakage tests through cracked

concrete elements, waterstop testing and compaction level tests for concrete construction

joints.

6.1 FLOATING BRIDGE HISTORY

Floating bridges have been an important element of the transportation system for

the Puget Sound and Seattle, Washington area for over 60 years. Lwin (1993b) stated

that floating bridges have been constructed to cross wide bodies of water where the depth

of water is very great or the soil bottom is too soft making conventional bridges too

expensive. Lwin et al. (1984) discussed a relative cost analysis performed during the

replacement of the west half of the Hood Canal Floating Bridge in the early 1980's. The

relative cost of the floating bridge replacement was at least two-and-a-half times less

expensive than a conventional fixed bridge. Lwin (1993b) stated that experience has

shown prestressed concrete bridges are an economical, durable and low maintenance

bridge solution.

6.2 HOOD CANAL DESIGN AND CONSTRUCTION

The west half of the Hood Canal Floating Bridge sank under high winds in 1979.

Lwin et al. (1984) speculated that the failure could have been caused by dynamic loading

due to wind and waves, slippage of the anchors, ponding of water on the pontoon decks

88

or water entering inside the pontoons. The west half was rebuilt and completed in 1982.

The undamaged east half was left unchanged at the time.

Typical pontoon dimensions of the east half of the Hood Canal Bridge were

described by Henley et al. (1997) as having widths of 50ft, heights of 14.3ft and pontoon

drafts of 9.2ft with post-tensioning only in the longitudinal direction. Nichols (1964)

discussed the construction process involved in pouring the pontoons for the bridge’s east

half. Concrete was poured through metal chutes to limit segregation. The maximum

concrete drop height from the end of the chutes was limited to five feet and was allowed

to spill out into the bottom slab area. The concrete was consolidated about 1 to 2 hours

after placement by allowing vibrators to sink of their own weight in the partially stiffened

mass.

Henley et al. (1997) discussed the dimension changes made to the Hood Canal

Bridge’s west half following the rebuilding after the 1979 storm. Typical dimensions of

pontoons for the west half of the bridge have widths of 60ft, heights of 18ft and pontoon

drafts of 12ft. The pontoons are post-tensioned transversely, vertically and

longitudinally. Lwin et al. (1984) described the construction of the west half of the

floating bridge following the storm. The pontoons used for the replacement west half

were divided into compartments 20ft wide by 30ft long. A 28day compressive strength of

6500psi was required. Coarse aggregate was limited to ¾ inch nominal maximum size.

Non-air entrained concrete was used. Pontoons consisted of “C” and “T” shaped precast

segments that were assembled by joining precast segments with cast-in-place concrete.

Pontoons were assembled in graving docks and floated to the site.

89

6.3 MIX DESIGN

The mix design used for the Lacey V. Murrow Floating Bridge in 1991 has

performed well in the field and will be used for the Hood Canal East Half Replacement

Project. Lwin et al. (1995) stated that the LVM mix was designed towards water-

tightness and durability because of their importance in the long-term performance of a

floating structure exposed to water and severe environmental conditions. The LVM mix

design is shown in Table 7.1. The report by Wiss, Janney, Elstner Associates, Inc. (1993)

found that water-tightness and durability are achieved through low water-cement ratios

and through the use of dense cement paste between aggregates.

Table 7.1 LVM Mix Design (after Lwin et al. 1995).

Weights per cubic yard (saturated,

surface-dry)

Concrete Constituent lbs.

Type II Portland cement 624

Silica fume (AASHTO M307)

50

Fly ash (AASHTO M295) 100

Paving sand 1295

Coarse aggregate 1770

Water 255

Water Reducing Agent

(ASTM C494), ounces

25

Superplasticizer (ASTM

C494), ounces

131

Air entrainment: none

Water/cement ratio 0.33

Slump, in 7

The report also found that the maximum water-cement ratio to limit concrete

permeability should be 0.33. The required LVM mix strength was 6500psi and was

easily achieved. Non-air entrained concrete was used for the pontoons because of the

mild climate. A maximum coarse aggregate size of a ½ inch was specified but a 3/8-inch

90

aggregate was ultimately used because of availability. To improve bond across the

construction joint the surface of the hardening concrete was water-blasted to expose the

aggregate. The roughening of the surface was reported to enhance the chemical adhesion

and mechanical interlock across the joint. Lwin et al. (1995) stated that a slump of seven

to nine inches was used for the mix and produced a flowable concrete that provided good

workability.

The LVM mix was designed after failure of the first Lacey V. Murrow Bridge in

1990. Lwin et al. (1994) described that the new mix was made using high performance

silica fume concrete to assure low permeability and shrinkage, thereby reducing the risk

of another failure. To further lessen the danger of failure individual cells were isolated

from adjacent cells to reduce the risk of flooding multiple cells in the event of a leak. As

another safety precaution Lwin (1993a) stated that individual cells were monitored by

sensors installed in each watertight compartment for early detection and warning of water

entry. An alarm would sound in the event of a leak notifying personnel to start the bilge

pumps. All the aforementioned safety improvements in addition to others were

implemented based on recommendations of a Blue Ribbon Panel, established after the

sinking of the Lacey V. Murrow Bridge in 1990.

6.4 WATER LEAKAGE TESTS THROUGH CRACKED CONCRETE

ELEMENTS

Dusenberry et al. (1993) performed tests on water flow rate through a cracked

reinforced concrete element. The dimensions of the concrete test sections were

predetermined as was the placement of reinforcement within the test specimen. The

91

reinforced specimens were cast monolithically and allowed to cure for seven days before

being physically cracked using hydraulic jacks.

A hydraulic head of 2.13m was applied to the crack face. The pressure was

applied to the specimen through a pressure chamber attached to the top surface of the

specimen. The pressure was maintained by an elevated reservoir with a continuous water

supply and overflow tube as shown in Figure 7.1. Water flow rate through the crack was

measured by recording the weight of collected water in a tarred pan placed beneath the

specimen over a measured time period.

Dusenberry et al. found that the equation Q = T * dh/dl where T is transmissity

and dh/dl is the hydraulic gradient through the wall thickness for smooth planar cracks

with parallel surfaces can be modified by an adjustment factor for non-smooth surfaces.

The adjustment factor reduces flow through new cracks smaller than 0.5mm and is partly

caused by roughness within the crack. The adjustment factor C is expressed as,

C = K(1-b

0

/b)

3

where K = 0.118, b

0

= 0.013mm and b is crack width in millimeters.

Figure 7.1 - Test configuration (after Dusenberry et al. 1993).

Constant

reservoir

elevation Overflow tube

Pressurized tank

Jacking

Jacks for crack

Width control

Water collection pan

Notches to induce

crack

(

sealed for test)

Concrete

specimen

92

Rashed et al. (2000) presented the results of the experimental phase of a research

program into the behavior and design of partially prestressed concrete water containment

structures. Typical wall sections were 250mm (9.84in) thick. The wall sections were

cracked using hydraulic jacks. A 300 by 1000mm plexi-glass chamber was fixed to the

top of the concrete specimen as shown in Figure 7.2 and filled with pressurized water

from a cylindrical steel container. Air pressure equivalent to 8-10m head of water was

applied to the water through the pressure regulator. A pressure of 70kPa (10.15psi) was

applied on the joint.

Figure 7.2 - Leakage test setup (after Rashed et al. 2000).

Water was collected from the underside of the joint and transferred to a graduated

cylinder. The volume of water collected was recorded manually together with the

corresponding time. Additionally, the leakage rate was recorded using load cells located

beneath the pressurized water container that measured the decreasing container water

weight. The weight of water lost was recorded electronically along with the

corresponding time.

Pressure chamber

Plexi

-

glass

)

drip pan

Hold down frame

The Specim

en

93

Under a constant pressure of 70kPa specimens were subjected to a hydraulic

jacking force until leakage occurred. Leakage began for an average crack width of

0.1mm from the north side and 0.03mm from the south side of the specimen in only a few

minutes. Once leakage occurred jacking was stopped and water loss measurements were

taken until water penetration stopped at which point the jacking force was increased and

the process continued. Leakage rates were initially low and decreased with time. For

through cracks with effective widths less than 0.15mm, the cracks leaked initially and

then self-sealed. Cracks with wider effective widths flowed continuously.

Clear (1985) performed tests to observe autogenous healing in concrete

specimens. Autogenous healing of concrete reduces the flow of water through a crack at

rates primarily affected by the width of the crack. Initial reduction in flow is due

primarily to blockage of the flow path by loose particles already in the crack that is later

enhanced by precipitation of calcium carbonate.

Site observations were performed on an existing water reservoir three-and-a-half

months old. Moisture was collected from two existing cracks in the walls of the reservoir

using aluminum gutters. Flow rates were determined by recording the time necessary to

collect a measured volume of water. Flow was recorded during the filling of the reservoir

and for the following two weeks when the cracks were subject to a constant head of

water. After the maximum water level in the tanks was reached the flow rates decreased

with time at an ever-decreasing rate.

A lab experiment was also performed to observe autogenous healing in a 150mm

3

concrete block. The block was cracked two days after casting through the use of jacking

bolts embedded in the concrete. The specimen was jacked until surface widths of 0.1, 0.2

94

or 0.3mm were observed. A hydraulic gradient of 22.5 was selected for the program to

represent a severe case (height of fluid column/thickness of wall) and was obtained using

a constant-head water tank attached to the entrance of the specimen. An elevation head

of 3.37m of water was maintained. Water passing through the crack was collected and

the time recorded to determine flow as shown in Figure 7.3. After seven days of flow,

each crack specimen was dismantled so that material within the crack could be examined.

Figure 7.3 - Cross-section of testing experiment (after Clear 1985).

The leakage of water through cracks in concrete is mainly proportional to the

effective width of the crack. The smaller the initial effective width, the faster the crack

will seal. The healing mechanism is a combination of mechanical blocking and chemical

precipitation of calcium carbonate. Results revealed that filling the reservoir slowly

could significantly reduce the total loss of water from the reservoir.

plasticine

sill to divert

water as it leaves

crack

collecting vessel

adhesive

water supply

and filter

manometer

95

6.5 MOIST CURING AND PERMEABILITY

Tan et al. (1995) performed tests on 100mm by 100mm cube specimens of

concrete aged two months to determine the desirable moist curing conditions necessary to

limit permeability. The testing faces were brushed before a water pressure was applied to

the face of the tested specimens as shown in Figure 2.4. Pressure heads of 0.3, 0.5, and

0.7 MPa were applied for the 1

st

, 2

nd

, 3

rd

day respectively. Specimens were split at the

conclusion of testing to determine their penetrating fronts. Tests revealed that specimens

cured in water for two days did not show significant differences in permeability as those

cured in water for six days. Only specimens soaked for 28 days showed significant drops

in concrete permeability. In all cases, the silica fume concrete had a much higher

resistance to water penetration than the specimens without.

Figure 7.4 - Test setup for water penetration test (after Tan et al. 1996).

Pressured water

inlet

Tube

Steel

Plate

Testing cell

Specimen

Bolt

Nut

96

6.6 WATERSTOP TESTING

Tatro et al. (1988) summarized techniques for replacing damaged waterstops,

primarily in dams. Waterstop failures are generally attributed to excessive movement of

the joint which ruptures the waterstop, honeycomb areas adjacent to the waterstop

resulting from poorly consolidated concrete, contamination of the waterstop surface

which prevents bond to the concrete, punctures of the waterstop or complete omission

during construction and breaks in the waterstop due to inadequate or non-existing splices.

The life of a waterstop is related to the relative movement across the joint. As the

movement increases the life of the waterstop decreases.

Wallis’ (1992) paper looks into efforts to decrease or eliminate water penetration

through underground tunnel walls. Water penetration can cause safety hazards through

freezing and unsightly stains. Wallis (1992) reported that water will always find a path

around obstacles and creating an impermeable barrier (waterproofing membrane)

between water source and protected environment is most cost effective and secure

method of ensuring a watertight underground structure.

Kishel (1989) performed tests to study the cost effectiveness of providing a lining at

contraction joints between concrete slabs that make up the lining of a canal. The linings

are often waterstops or sealants applied to the joint to limit water leakage. Seepage rate

tests were performed on an unlined concrete canal in Arizona. Information was also

available for two canals located within 100 miles of the test site that were lined with

polyvinyl chloride strips or elastomeric sealant.

Evaporation of water from the canal was determined through the use of a class A

Weather Service evaporation pan that was installed next to the pan in a secure area. The

97

seepage rate for the unlined canal was calculated as 0.036ft

3

/ft

2

/day. The seepage rate for

the two canals with linings was found to range between 0.0110-0.090ft

3

/ft

2

/day. The

open jointed canal rates were within the range of the sealed joint canal. The value of

water saved over a 20- or 30- year payback period would be less than the cost of sealing

at present cost levels. Observed rates indicate a lack of economic justification for

providing contraction joint sealing.

6.7 COMPACTION LEVEL FOR CONCRETE CONSTRUCTION JOINTS

Liou (1996) described tests to determine the effects of construction joints in the

Kawasaki man-made island in the center of Tokyo Bay. The island was so extensive that

the concrete for the basemat-of the island would have to be completed in several pours.

The tests were designed to simulate the worst conditions that could be experienced in the

field. They wanted to determine the best placing schedule and compaction level for the

concrete to produce the best joint. The joint was evaluated in terms of compressive

strength tests of cylinders and when testing initial vibration, slump tests were also

performed.

The concrete used in the tests was too flowable to allow meaningful conventional

slump data to be gathered. The worst-case condition experienced in the field was for a

joint that formed a 45-degree angle. Liou (1996) found that compaction of concrete

layers seems to have a beneficial effect on the compressive strength of the large-sized

concrete specimen (150mm diameter, 300mm high). Tests showed that placement delay

times longer than four hours seemed to have a slight detrimental effect on the strength.

Also, the initial vibration of the concrete delays the hardening process in the concrete and

prolongs its workability over time.

98

Loiu (1996) reported that the level of compaction was simulated by either striking

a concrete layer with a standard stick a predetermined number of times or by introducing

a small vibrator into the concrete layer. A test specimen that simulated a medium

compaction level in the field received 10 stick strikes in each of the two casting layers of

concrete; while a test specimen that simulates maximum compaction level in the field

received 25 stick strikes per layer. When a vibrator was used it was carefully introduced

into the sample at several equally spaced points for a total vibrational duration of 40

seconds. This helped to obtain uniform compaction and to avoid segregation in the

sample. Results showed that vibration provided by a small vibrator generally had a better

effect than vibration provided by using a striking rod.

6.8 SUMMARY

The literature review has revealed that limited research is available on joints in

floating bridges. The main reasoning for this limited information is due to the fact that

only a limited number of floating bridges exist in the world. It is evident from this

limited literature that there have been two approaches to deal with water penetration

through concrete joints. The first one is the use of special material added to the joint that

act as water stoppers or barriers to water flow. The chemical composition, placement and

application processes of these materials vary significantly. The second approach is to

allow the rough surfaces of concrete joints to act as barriers for the flow. The

experimental plan in the remaining parts of this thesis investigates the effectiveness of

these two approaches in reducing or eliminating water infiltrations through joints in

floating bridges.

99

CHAPTER 7: MATERIALS AND TESTING METHODS

7.1 MIX DESIGN SPECIFICATIONS

The mix design for the reconstruction of the Lacey V. Murrow Floating Bridge

across Lake Washington was used for this project. The mix was chosen based on its

water-tightness, durability and low permeability. The mix was modified to use only a

superplasticizer, Glenium 3000 NS instead of the normal and high-range water reducers.

The materials needed to produce the test specimens were shipped from mixing plants

around the state to Washington State University. Table 8.1 contains the mix design

chosen for the laboratory experiments. The final mix prepared at Washington State

University is described in Table 8.2.

7.2 TEST SPECIMENS

Specimen dimensions were chosen after studying a typical joint in the Hood Canal

Floating Bridge. The joint had a thickness of 18 inches with a 3/4in deep by 9-inch long

keyway centered within the joint as shown in Figure 8.1. Test specimen dimensions were

reduced because of space and weight considerations. Specimens needed to be small

enough to construct and store within a tight work area and be light enough to allow easy

handling. Smaller dimensions produced a worst-case scenario because the wall

thickness, and therefore the distance water must travel through the joint would be far

greater in the field.

Specimens were 8 inches thick, 16 inches long and 12 inches tall. A construction

joint was placed halfway up the height and contained a 1/2in deep by 3-inch wide

keyway centered in the specimen's depth. Two thin steel plate’s 1/8in thick, 8 inches

100

wide and 16 inches long were bonded to the freshly poured concrete at the top and

bottom of the 12in tall specimen. Figure 8.2 shows the dimensions and layout of a

typical specimen. The plates were designed to help hold the freshly poured concrete in

place and distribute the pressure applied to two 7/8in steel bars embedded into the

concrete. The steel bars were attached to nuts welded to the bottom steel plate. Two

one-inch diameter openings in the top steel plate were provided to allow the bars to slide

through. Schematics of the steel plates are shown in Figure 8.3.

The steel bars were spaced 8 inches on-center at the center of the specimen's

thickness. The bars were threaded over the bottom one-inch of length to allow threading

into nuts welded to the bottom plate. Threading was provided over the top 19 inches of

the 30in bar length to allow threading of a nut. Figure 8.4 shows a picture of the steel

bars and lower plate.

Specimens were cast within forms built for the experiment. The forms were

connected together to make the necessary dimensions. Two sets of forms were created

for each specimen. The first set was 6 inches tall while the second set was 12 inches tall.

The 6-inch forms created a box placed over the lower steel plate. The two 7/8in steel

bars were connected into the plate and a one-inch diameter PVC tube was placed around

the steel bars. The tube separated the concrete from the steel reducing the chances of

small stress cracks near the steel. The tubes were cut just long enough to measure 12

inches when added to the height of the nuts they rested on. Figure 8.5 shows the

placement of forms around the steel bars and the location of the PVC tubes covering the

steel bars.

101

Six 10in long carriage bolts were embedded into the specimen's face. The bolts

were applied in a circular pattern with the construction joint located in the center. The

bolts were needed to attach a pipe with flanged fitting to the face of the specimen. The

pipe supplies a water pressure to the face of the specimen. Holes were drilled into the

forms in the locations of the flange's boltholes. The carriage bolts were embedded

halfway into a specimen's depth with a 1/2in flat washer glued to each bolt to provide

additional pullout resistance.

Concrete compaction and smoothing completed the construction of the initial

concrete pour. A hand trowel was used to smooth the surface of the joint and to create the

keyway shown in Figure 8.6. The 6-inch specimens were placed near wet burlap and

covered for 24 hours to cure. After the 24-hour period ended specimens were removed

from the 6-inch forms and the 12in forms were fastened in place.

The final pour of concrete was 48-hours after the completion of the initial pour.

The concrete was compacted and smoothed by hand trowel. The top steel plate was fitted

over the 7/8in steel bars and firmly pressed down onto the freshly poured concrete.

Specimens were placed beside wet burlap and covered for 24-hours to cure. After 24

hours specimens were removed from the forms creating a finished specimen as shown in

Figure 8.7.

Two 60ton hollow plunger cylinders were used in unison to tension the 7/8in steel

bars of each specimen simultaneously. A nut was threaded the full 18 inches onto the

steel bars. The nuts were threaded until hand-tight against the steel plate. A steel spacer

was then placed over the bars to provide room for tightening the nuts after jacking. The

hydraulic cylinders were placed over the bars to rest on the spacer. A one-inch thick steel

102

bar with two one-inch circular openings was placed over the cylinders. Finally a nut was

threaded down the 7/8in bars to the one-inch thick steel bar. The post-tensioning setup is

shown in Figure 8.8.

The nuts were tightened against the one-inch thick steel bar before the hydraulic

cylinders were loaded. A hand pump with pressure gauge was used to load the cylinders.

The two cylinders were attached to the hand pump by a pressure T that applied an equal

pressure to both cylinders. The cylinders were loaded slowly forcing the one-inch steel

bar and top nuts upward applying tension to the 7/8in steel bars. The system was loaded

to a 3000psi gauge pressure reading on the hand pump before the bottom nuts were

tightened and the pressure was released from the cylinders. The top nuts, one-inch thick

steel bar, hydraulic cylinders and steel spacer were then removed from the specimen.

The process was repeated with all post-tensioned specimens. Loading of each specimen

took a few minutes to complete.

Each post-tensioned bar was assumed to apply a pressure to the concrete over a

confined area 3 inches in diameter. The thin steel plate resting on the specimens was too

thin to effectively distribute the applied pressure after the force was transferred from the

cylinders to the steel bars. The pressure applied to the concrete by the jacking force was

calculated as 5402.78psi by the equation:

P = (P

j

* A

hc

* N) / A

e

(8.1)

where:

P = pressure applied to the specimen (psi),

P

j

= pressure supplied by hand pump to cylinders (3000psi),

A

hc

= effective area of one hydraulic cylinder (12.73in

2

),

103

N = number of cylinders (2),

A

e

= area of concrete effected by one hydraulic cylinder (assumed 3in diameter effective

area =7.07in

2

).

The 5402.78psi pressure applied to the concrete is much higher than that seen in

the field. The pressure applied to the joint in the field is about 450psi at the joint. This

was determined based on a 180kip force applied by tendons spaced 2ft on-center. The

original pressure supplied by the hand pump was determined assuming that the force

applied to the specimens would be applied over the entire surface of the specimens. The

pressure this would have applied to the specimens assuming losses totaling 25% from the

jacking system was 447psi. The plates located at the top and bottom of the specimens

were too thin to effectively distribute the pressure throughout the specimen, hence the

high-pressure concentration.

The increased compressive stress around the steel bars should not affect the

results. The increased stress was over a very small area that increased the stress in that

area but should not have significantly increased the stress in the surrounding areas. This

increased stress would affect water penetration through the joint within this elevated

compression area but should not affect the surrounding areas of the joint. The majority of

the joint was unaffected by the increased compressive stress and would have functioned

normally.

104

Table 8.1 Mix Design

Weights per cubic yard (saturated,

surface-dry)

Concrete Constituent lbs.

Type II Portland cement 624

Silica fume (AASHTO M307)

50

Fly ash (AASHTO M295) 100

Paving sand 1295

Coarse aggregate 1770

Water 255

Water Reducing Agent

(ASTM C494), ounces

none

Superplasticizer (Glenium

3000 NS), floz/cwt

4-12

Air entrainment: none

Water/cement ratio 0.33

Slump, in 7-9

Compressive Strength, f'c, psi

6500

105

Table 8.2 Final Mix Design

Weights per cubic yard (saturated,

surface-dry)

Concrete Constituent lbs.

Type II Portland cement 624

Silica fume (AASHTO M307) 50

Fly ash (AASHTO M295) 100

Paving sand 1295

Coarse aggregate 1770

Water 255

Water Reducing Agent

(ASTM C494), ounces

none

Superplasticizer (Glenium

3000 NS), floz/cwt

5.50

Air entrainment: none

Water/cement ratio 0.33

Slump, in 8

Compressive Strength, f'c, psi

8788

106

Figure 8.1 - Keyway dimensions in field (after Hood Canal Retrofit and East-half

Replacment Construction Plans: SEC C-C).

107

Figure 8.2 - Test specimen dimensions.

108

Figure 8.3 - Dimension specifications for the steel plates.

109

Figure 8.4 - Steel Bars 7/8in diameter screwed into bottom plate.

THREADED

BAR

WELDED

NUT

7/8”

BAR

STEEL PLATE

110

Figure 8.5 - Construction setup for initial concrete pour.

FORMS

PVC

111

Figure 8.6 - Completed keyway of initial pour.

KEYWAY

112

Figure 8.7 - Completed test specimens.

113

Figure 8.8 - Hydraulic cylinder setup for post-tensioning the specimens.

NUTS

STEEL BAR

HYDRAULIC

CYLINDER

STEEL

SPACER

NUTS

HAND

PUMP

114

7.3 PRODUCTS AND CONSTRUCTION METHODS TESTED

Products chosen for testing were determined based on manufacturer's

recommendations and available product data sheets. Tested products included waterstops

designed to prevent water penetration by forming a preventive barrier within the joint and

a cement coating designed to prevent water penetration by forming a barrier outside the

joint. The chosen products are listed in Table 8.3.

The construction methods chosen for laboratory testing were based on

recommendations from the Washington State Department of Transportation (WSDOT

2001) and companies within the concrete industry. The different methods were designed

to decrease water leakage at the joint by either; improving bond across the joint,

increasing the surface area that water must follow to pass through the joint or by

improving compaction at the joint. The construction methods chosen are listed in Table

8.4.

115

Table 8.3 - Products tested in experiments.

Product Company

Advantages Placement

MC-

2010MN

(Waterstop)

Adeka

Ultra Seal

USA

expands upon contact with water,

forms water barrier

within keyway on

negative pressure side of

7/8in steel bars

Synko-flex

(Waterstop)

Henry

adhesive waterstop, bonds to

freshly poured concrete during

curing, forms water barrier

within keyway on

negative pressure side of

7/8in steel bars

Waterstop-

RX 101TRH

CETCO

expands upon contact with water,

forms water barrier

within keyway on

negative pressure side of

7/8in steel bars

Tegraproof

(Coating)

ChemRex

slurry coat, seals wall-floor joints

brush applied to external

face of specimen in direct

contact with water

pressure

Table 8.4 - Construction methods tested in experiments.

Construction

Method Procedure Advantages Placement

Mortar/slurry

3 parts sand to 1 part cement

plus water (WSDOT 2001)

greater

compaction at

joint

first two inches

of final pour

Preco HI-V

Retarder (Master Builders),

brush applied to joint

surface

exposes aggregate

at joint, improves

bond strength

freshly poured

joint surface of

initial pour

Raking Method

0.5in deep grooves 1.5

inches on-center

(perpendicular to water

flow)

lengthens water

path through joint

freshly poured

joint surface of

initial pour

116

Figure 8.9 - Waterstop placement within construction joint of specimen.

WATERSTOP

117

Figure 8.10 - Tegraproof coating placed on exterior joint face.

COATING

118

71.3.1.2

Figure 8.11 - Mortar/slurry grout over initial two-inch depth of the second pour.

CEMENTITIOUS

GROUT

119

71.3.1.3

71.3.1.4

Figure 8.12 - Exposed aggregate along surface of joint caused by Preco HI-V.

EXPOSED

AGGREGATE

120

7.4 EXPERIMENT 1

Experiment one involved exposing specimens to a constant water pressure similar

to that experienced in the field. A typical pontoon for the Hood Canal Floating Bridge

has a draft of 13ft. The horizontal construction joint studied was located 28in from the

base of the pontoon creating a joint 128 inches or 10.67 feet below the water line. The

water elevation of 128 inches corresponds to a pressure on the joint of 19.44psi. The

pressure was determined by the equation:

P = γh + P

0

(Young et al. 1997)) (8.2)

where:

P = pressure on joint (psi),

γ = specific weight of fluid (salt water 64lb/ft

3

(Young et al. (1997))

h = water elevation height (in)

P

0

= atmospheric pressure (assumed 14.7psi (Young et al. (1997))

The 19.44psi pressure was supplied to the system by means of an elevated water

reservoir with water elevation 128 inches above the surface of the specimens. The

reservoir consisted of an 18in diameter PVC cap fastened to the ceiling. Water entered

the reservoir through a constant inflow tube attached to the bottom of the cap. Water was

supplied from a second reservoir located at the ground surface by a small 1/30hp

centrifugal pump located on the ground. A tube was attached to the side of the elevated

reservoir 128in above the surface of the specimens. The tube served as an overflow pipe

for the upper reservoir and returned any excess water to the lower reservoir. The lower

reservoir consisted of a plastic 55-gallon barrel filled with salt water from the Hood

121

Canal Floating Bridge. The system created was self-maintained and could be left

unmonitored overnight.

Six flexible tubes were connected to the bottom of the elevated reservoir. The six

tubes ran to different specimens. The tubes were connected to a 6-inch PVC cap glued to

an 18in long PVC pipe. The PVC pipe was glued to the inside of a flanged fitting with

eight bolthole openings. The PVC pipe was bolted to the side of the concrete specimens

with the pipe centered on the joint.

The flanged fittings glued to the six-inch PVC pipe were connected to the

concrete specimens by 10in long carriage bolts embedded into the concrete. Additional

pullout resistance was supplied by gluing 1/2in flat washers to the carriage bolts. Six

carriage bolts were embedded into each specimen because of limited spacing. A

neoprene gasket was placed beneath the flanged fitting to prevent water leakage at the

interface between the flange and concrete. The test setup is shown in Figure 8.13.

The system was designed to test up to six specimens simultaneously. Fewer

specimens could be tested because 1/2in ball valves were connected to each specimen

setup above the 6-inch cap. The valves could be closed to prevent water flow from tubes

unconnected to specimens. The valves also allowed lines to be closed once leakage

occurred to prevent pressure loss from the system.

A 3/8in bleed-hole was drilled into the 6-inch PVC cap. The bleed-hole allowed

air to escape the system when water was being added. Once water began escaping

through the bleed-hole the valve was closed and a 3/8in bolt with Teflon tape covering

the threads was tightened in the opening. The ball valve was then reopened to finish

filling the system with water. Specimens were shaken to remove any additional air

122

trapped beneath the six-inch PVC cap. Air bubbles were allowed to escape through the

top of the reservoir. The pressure system connection to the test specimens is shown in

Figure 8.14.

Hood Canal water was used for the experiment to ensure pressures similar to

those experienced in the field. The supplied pressure was equivalent to the 19.44psi

experienced in the field because the same fluid was used in the laboratory and the water

elevation was held at 128 inches above the specimen. Any atmospheric pressure

differences were ignored.

Specimens were placed on their sides in the testing apparatus to allow the water

pressure supplied by the 6-inch pipe to be applied vertically. Specimens were placed on

two 3.5-inch square wood beams located 14 inches apart on-center. The beams rested on

cinder blocks that raised the specimens two feet off the ground allowing a large funnel to

be placed beneath the specimens. The funnels were 18in diameter barrel funnels

positioned beneath the specimens to catch water escaping through the specimens.

Additional room was provided for a visual inspection of the underside of the specimens

and to provide space for a small water collection beaker. Two people were needed to lift

specimens onto the setup. The water collection system located beneath the specimens is

shown in Figure 8.15.

Stage 1

Stage one consisted of four specimens. The four specimens included two controls

one with a construction joint and one without as well as two waterstops MC-2010MN and

Synko-flex as shown in Table 8.5. The four specimens were post-tensioned nine days

after the second concrete pour. Specimens were compacted by mechanical stinger

123

repeatedly lowered into the freshly poured concrete for 30 seconds. Specimens were

tested for 15 days with monitoring every 24 hours to observe water leakage. The time

corresponding to when leakage occurred was recorded.

Table 8.5 - Stage one specimens.

Stage 1

Product

Placement

Construction/Application

Control (No Joint)

N.A.

specimens completed in one pour, mechanical

vibration of concrete

Control

(Construction

Joint)

N.A.

specimens completed in two pours, mechanical

vibration of concrete

MC-2010MN

Waterstop

within keyway on

negative pressure

side of 7/8in steel

bars

two concrete pours, mechanical vibration of

concrete; applied continuous bead of P-201

paste to the joint and allowed to cure for 24

hours before pressing MC-2010MN into the

paste.

Synko-flex

Waterstop

within keyway on

negative pressure

side of 7/8in steel

bars

two concrete pours, mechanical vibration of

concrete; brush applied Synko-flex primer to

surface and allowed to dry 3 hours. Peeled

release paper from one side of Synko-flex strip

and press firmly onto primed surface.

124

71.4.1.1

71.4.1.2

Figure 8.13 - Experimental setup of the first experiment.

UPPER

RESERVOIR

LOWER

RESERVOIR

PUMP

TEST

SPECIMENS

125

Figure 8.14 - Specimen connection to pressure system.

FLANGED

FITTING

PVC CAP

BLEED HOLE

CARRIAGE

BOLT

126

Figure 8.15 - Water collection system located beneath specimens.

FUNNEL

BEAKER

127

7.5 EXPERIMENT 2

Experiment two involved placing a variable pressure on the system. The setup of

experiment one was modified for use in experiment two. The pressure applied by the

system needed to be significantly increased so the upper reservoir of experiment one was

removed and an air pressure system was installed in its place.

Experiment one's testing setup was modified by removing the reservoirs and

flexible tubing from the system. The experimental setup of the second experiment is

shown in Figure 8.16. Air pressure was applied to the specimens by a 2-inch diameter

galvanized steel pipe suspended above the specimens. Openings were placed every 18

inches along the galvanized pipe. A 2-foot long by 1/2in inner diameter clear plastic tube

was securely fastened to the galvanized pipe as shown in Figure 8.17. Polyethylene hose

with 1/2in outer diameter by 0.375in inner diameter was connected to the clear tubing

and ran to the 1/2in ball valve of the original system. The polyethylene hose could hold a

water pressure up to 123psi.

One end of the 2-inch diameter galvanized pipe was capped while the opposite

end was connected to an air compressor by means of an air pressure hose. The hose was

connected to a valve used as a shutoff for the system. The setup also included a pressure

gauge and regulator used to increase and decrease pressure on the system as shown in

Figure 8.18.

Water was added to the system after specimens were attached to the flanged

fittings. The system was initially designed to allow water to be pumped into the

galvanized pipe from the lower reservoir by means of a seventh connection to the

galvanized pipe. Water was not pumped through the galvanized pipe because of the high

128

probability of corrosion. The valve connected to the seventh line was shut to prevent air

leaks from the system through the open line. Water was poured into the system through

funnels at the connections between the galvanized pipe and tubing.

The bleed-hole was used to release trapped air as the specimens were filled with

water. After all air was removed from the line the water level was increased to a mark 4

feet above the surface of the specimens. The initial pressure on the specimens due to

water elevation and atmospheric pressure was 16.48psi. Any air pressure added to the

system was directly added to the initial pressure to obtain the total pressure on the

system.

Air pressure on the system was increased until leakage occurred in all specimens.

The valves were closed once leakage occurred to prevent pressure loss from the system.

The leakage was recorded and used to determine the relative success of different

products.

Stage 1

The specimens of stage one were re-tested using the variable air pressure system

of experiment two. Stage one specimens were tested in experiment two, three months

after initial casting. Air pressure on the system was initially zero and was increased every

half hour to a maximum air pressure of 100psi.

Stage 2

Six specimens were cast in stage two constructions. The specimens consisted of

the three waterstops; MC2010MN, Synko-flex and Waterstop-RX 101TRH as well as

three specimens where the mortar/slurry was added over the first two inches of the

second pour as shown in Table 8.6. The three waterstops were placed on the exposed

129

joint one-day after initial curing. Waterstops were placed 24 hours before submersion in

tap water for five days. Specimens were then removed and allowed two days of drying

before completion of the second pour of concrete.

Table 8.6 - Stage two specimens.

Stage 2

Product

Placement

Construction/Application

MC-2010MN

Waterstop

within keyway on

negative pressure

side of 7/8in steel

bars

two concrete pours, mechanical vibration of

concrete; applied continuous bead of P-201

paste to the joint and allowed to cure for 24

hours before pressing MC-2010MN into the

paste.

Synko-flex

Waterstop

within keyway on

negative pressure

side of 7/8in steel

bars

two concrete pours, mechanical vibration of

concrete; brush applied Synko-flex primer to

surface and allowed to dry 3 hours. Peeled

release paper from one side of Synko-flex strip

and press firmly onto primed surface.

Waterstop-RX

101TRH

within keyway on

negative pressure

side of 7/8in steel

bars

two concrete pours, mechanical vibration of

concrete; brush applied WB-ADHESIVE to

joint surface, allowed to dry for 20 minutes

before waterstop pressed onto surface

Mortar/slurry over

normal joint

applied to first two

inches of second

pour

two concrete pours, mechanical vibration of

c

oncrete, initial pour was normal. Mortar/slurry:

91lbs sand, 30lbs cement, 9.9lbs water and 5mL

superplasticizer

Mortar/slurry

applied over

exposed aggregate

surface caused by

(Preco HI-V)

Preco HI-

V retarder

to joint surface,

Mortar/slurry

applied to first two

inches of second

pour

two concrete pours, mechanical vibration of

concrete, initial pour had Preco HI-V applied to

freshly poured surface for 24 hours before being

washed off. Mortar/slurry: 91lbs sand, 30lbs

cement, 9.9lbs water and 5mL superplasticizer

Mortar/slurry

applied over raked

joint surface

Grooves cut into

joint surface of

initial pour,

Mortar/slurry

applied to first two

inches of second

pour

two concrete pours, mechanical vibration of

concrete, initial pour contained no keyway,

grooves cut into freshly poured concrete. 1/2in

deep by 1-1/2in on-center, Mortar/slurry: 91lbs

sand, 30lbs cement, 9.9lbs water and 5mL

superplasticizer

130

The mortar/slurry was placed at the time of the second pour of concrete. The

mortar/slurry was applied to the first 2 inches of the second pour. Construction methods

differed for the initial pour of concrete for each of the three specimens. One specimen

consisted of a typical initial pour of concrete as described in section 8.2. The next two

specimens were designed to increase the surface area along the joint of pour one, thereby

improving bond strength and forcing water to follow a longer path to penetrate through

the specimen. One specimen had Preco HI-V, a chemical retarder used to expose

aggregate, applied to the freshly poured joint surface of pour one. The second specimen

used a raking method to create grooves in the concrete surface perpendicular to the flow

path of water through the specimen. No keyway was used with the raking method;

instead grooves were cut in the flat joint surface by dragging a thick wire through the

freshly poured concrete. The vertical grooves were a 1/2in deep and spaced an inch-and-

a-half on-center.

The six specimens of experiment two were tested two-and-a-half months after the

final concrete pour. The specimens were post-tensioned and tested on the same day.

Specimens were compacted by mechanical stinger lowered into the freshly poured

concrete for 30 seconds. Air pressure on the system was initially zero and was increased

every half hour to a maximum air pressure of 100psi.

Stage 3

Six specimens were tested in stage three. The six specimens included one control

joint, the Tegraproof coating brush applied to the external surface of the specimen in

direct contact with the water pressure and a 2-inch thick mortar/slurry placed over a

normal initial concrete pour. Additional specimens included the Preco HI-V retarder

131

applied to the joint surface of the initial concrete pour, and two waterstops: MC2010-MN

and Synko-flex as shown in Table 8.7. The specimens of stage three were tested 29 days

after the final pour of stage three.

Table 8.7 - Stage three specimens.

Stage 3

Product

Placement

Construction/Application

Control

(Construction

Joint)

N.A.

specimens completed in two pours, compacted

by 10 stick-strikes

MC-2010MN

Waterstop

within keyway on

negative pressure

side of 7/8in steel

bars

two concrete pours, compacted by 10 stick-

strikes; applied continuous bead of P-201 paste

to the joint and allowed to cure for 24 hours

before pressing MC-2010MN into the paste.

Synko-flex

Waterstop

within keyway on

negative pressure

side of 7/8in steel

bars

two concrete pours, compacted by 10 stick-

strikes; brush applied Synko-flex primer to

surface and allowed to dry 3 hours. Peeled

release paper from one side of Synko-flex strip

and press firmly onto primed surface.

Mortar/slurry over

normal joint

applied to first two

inches of second

pour

two concrete pours, compacted by 10 stick-

strikes, initial pour was normal. Mortar/slurry:

24lbs sand, 8lbs cement, 3.2lbs water

Preco HI-V

Retarder

Preco HI-

V retarder

applied to joint

surface to expose

aggregate

two concrete pours, compacted by 10 stick-

strikes, initial pour had Preco HI-V applied to

freshly poured surface for 24 hours bef

ore being

washed off.

Tegraproof

Coating

applied to surface

of specimen

directly exposed to

water pressure

two concrete pours, compacted by 10 stick-

strikes, Tegraproof mix: 10lb Tegraproof, 3.41lb

water; brush applied to wetted joint surface,

surface kept moist for 48 hours

No PVC tubing was placed around the 7/8in bars because the specimens were not

post-tensioned. Specimens were compacted by 10 stick-strikes of the slump rod during

each pour to reduce compaction at the joint and represent poor compaction that could

occur in the field during construction. The 1/8in steel plate placed on top of earlier

specimens was not used because no post-tensioning occurred. A concrete filler/sealant

132

was applied to the surface of the joint to ensure that water leakage would occur only

through the joint. The sealant was applied to the sides of the specimen and across the

specimen face, except in the area in direct contact with the water pressure as shown in

Figure 8.19. The back of the specimen was left uncovered to allow water penetration to

occur through the specimen.

133

Figure 8.16 - Experimental setup of the second experiment.

AIR PRESSURE

SYSTEM

134

Figure 8.17 - Connection of clear plastic tubing to galvanized pipe.

GALVANIZED

PIPE

CLEAR TUBING

FLEXIBLE

TUBING

135

Figure 8.18 - Pressure regulator for air pressure system.

GALVANIZED

PIPE

PRESSURE

REGULATOR

SHUTOFF

VALVE

AIR HOSE

136

Figure 8.19 - Concrete filler and sealant applied to the construction joint of stage

three specimens.

CONCRETE

MORTAR/SEALANT

137

7.6 EXPERIMENT 3: WATERSTOP TESTING

The Washington State Department of Transportation (WSDOT) was concerned

with premature expansion of the tested waterstops. An extended period of time could

elapse between the pouring of the first and second pours of concrete in the field.

Waterstops placed on the joint surface during the initial pour could be exposed to severe

environmental conditions that might cause waterstop swelling. WSDOT wanted to

ensure that for a worst case scenario (standing water on the waterstop) the waterstops

would not expand excessively before the second pour of concrete. Excessive expansion

of a waterstop before joint completion could lead to waterstop damage or failure.

Three samples of each waterstop tested in earlier experiments were cut into

200mm lengths for the experiment. One sample of each waterstop was placed in a plastic

container filled with tap water. Samples were completely submerged beneath the surface

of the water to simulate a submerged joint in the field. Waterstops that floated were

placed beneath plastic strips anchored beneath the water surface. Figure 8.20 shows the

experimental setup of experiment three.

Measurements of waterstop weight, length and thickness were taken at intervals.

Measurements were taken at day 0, 1, 3, 5, 7, 10, 14, 15, 20, 28, 31, 36 and 42. Samples

were removed from the containers and wrapped in paper towels to remove excess surface

moisture from the specimens before weighing. After all measurements were recorded

samples were re-submerged. Expansion rate determined by equation:

Expansion rate = (weight after soaking – weight before soaking) / weight before soaking.

138

Figure 8.20 - Testing setup of the third experiment.

CONTAINERS

139

CHAPTER 8: TEST RESULTS

8.1 MIX CHARACTERISTICS

The characteristics of the mix prepared at Washington State University were

described in Table 8.2. All specimens were prepared as closely to the LVM mix design

as possible. The amount of water reducer used per mix was slightly modified to create a

more workable mix. Concrete compressive strength and slump were determined for six

test cylinders made with the given mix. Slump tests and compressive strength tests were

not performed for each concrete pour due to the similarity between pours.

8.2 EXPERIMENT 1 TEST RESULTS

Four 8x12x16 inch concrete specimens were tested in the first experiment

according to methods described in section 8.3. The specimens tested in the first

experiment were two controls, one with and one without a construction joint and two

waterstops, the MC-2010MN product and the Synko-flex product. The specimens were

exposed to a water pressure of 19.44psi for 15 days. Specimens were repeatedly

checked over the initial two days of testing to observe leakage in the system. No leakage

was observed during the first two days of testing. Observations were taken once every 24

hours for the remainder of the test. Testing was stopped after 15 days because no water

leakage was observed through any specimen.

No leaks were observed from the pressure system connected to the specimens.

The water elevation in the system was held constant throughout the duration of the test.

The pump was able to transport water from the lower reservoir to the upper reservoir

without interruption.

140

The four specimens tested prevented water penetration through the joint for a

pressure of 19.44psi. The test was inconclusive in determining the effectiveness of a

given product at preventing water penetration through the joint. All specimens prevented

leakage including the control specimen containing a construction joint. The jointed

control should have been the first specimen to leak out of all specimens tested. The

inability to produce water leakage through the specimens showed that the pressure

supplied by the system was inadequate for determining the most effective product or

testing method for preventing water leakage.

The lack of water leakage from the test specimens at a pressure similar to those

experienced in the field that cause leakage shows that construction methods in lab were

better than those used in the field. The specimen joint had a much smaller thickness than

that in the field but was not exposed to the excessive stresses experienced in the field due

to wave and tidal fluctuations. A likely reason the specimens did not leak is improved

concrete compaction in the lab. Nichols (1964) stated that concrete in the field was

poured from significant heights over large areas before being vibrated. The lower drop

height, reduced specimen size, better access to the joint and the use of the LVM mix in

the lab all helped to improve joint construction, thereby reducing water penetration.

8.3 EXPERIMENT 2 TEST RESULTS

As discussed in Chapter 8, the setup of the first experiment was modified to apply

a variable air pressure to the system as described in section 8.4. A variable air pressure

system was used because the pressure that would cause leakage through the specimens

was unknown. Air pressure could be slowly increased until leakage occurred through the

joint. The initial water pressure on the system was 16.48psi. Air pressure applied to the

141

system would be added to the initial water pressure to compute the total pressure applied

to the specimens.

Stage One

The four specimens tested in the first experiment were retested in the second

experiment using the variable air pressure. Water levels within the clear plastic tubing

connected to the galvanized pipe were monitored and water heights recorded to determine

water volume decreases. Measurements were taken every half hour to determine

decreases in water volume and to observe any water leakage from the system, both

through the specimen and pressure system. Air pressures were increased every half-hour

from an initial pressure of zero to a final pressure of 100psi. The 100psi air pressure was

held on the system for 30 minutes before testing was completed.

Water volume decreases within the clear tubing at different air pressures are

shown in Figure 9.1. The same water volume decreases are shown for total pressure

changes in Figure 9.2. Measurements of water level changes were no longer recorded

after they fell below the clear tubing. Water level changes were taken immediately

before increasing the pressure. Decreases in water volume were seen in all four

specimens tested. Water volume changes were no longer recorded once water leaks

occurred within the pressure system of a specimen. The Synko-Flex waterstop specimen

experienced a leak in the pressure system after 5psi air pressure was applied to the

system. A leak was observed in the pressure system for the control specimen containing

construction joint at 25psi air pressure. The specimens all had similar water volume

changes when no leaks were observed in the pressure systems.

142

No water leakage was observed through the construction joint of the test

specimens at any pressure. Testing was stopped after 100psi air pressure was held in the

system for 30 minutes. Water leaks from the system did not significantly reduce air

pressure in the system. Pressures close to six times that experienced in the field were

applied to the joint without causing leakage. No leakage was observed through the

specimen showing that construction methods used in lab were better than those used in

the field. The specimens were too highly compacted to allow water leakage through the

joint.

The MC-2010MN specimen had water volume decreases very similar to the joint-

less control specimen even though one specimen contained a construction joint and one

did not. Neither specimen experienced a significant leak from their pressure systems.

The control specimen containing construction joint also had similar water volume

decreases before a pressure system leak was observed at an air pressure of 20psi. The

three specimens all had similar water elevation changes when there were no leaks in the

pressure system. The likely reason was the high level of concrete compaction caused the

second pour of concrete to completely bond to the initial concrete pour effectively

closing the construction joint.

143

Figure 9.1 - Water volume changes versus air pressure applied to stage one

specimens of the second experiment.

0

1000

2000

3000

4000

5000

6000

0 20 40 60 80 100 120

Air Pre s sure (ps i)

Volume (cm

3

)

Control, No Joint Control, Joint MC-2010MN

144

Figure 9.2 - Water volume changes versus total pressure on the system for stage one

specimens of the second experiment.

0

1000

2000

3000

4000

5000

6000

0 20 40 60 80 100 120

Total Pressure (psi)

Volume (cm

3

)

Control, No Joint Control Joint MC-2010MN

145

Stage Two

Six specimens were constructed for stage two testing. The six specimens

included the three waterstops; MC-2010MN, Synko-flex and Waterstop-RX 101TRH as

well as three specimens where a mortar/slurry mixture was added over the first two

inches of the second concrete pour to create the joint. The mortar/slurry was placed over

a normal joint, over an exposed aggregate surface created by the Preco HI-V retarder and

over a concrete surface that had been raked to form grooves in the concrete of the joint.

The six specimens were completed before testing was finished for the first experiment.

The specimens were constructed and compacted similarly to those of stage one.

The water elevation in each specimen setup was recorded. Air pressure in the

system was increased 10psi every 10 minutes for the length of the test. Testing began

with no air pressure on the system and concluded after 100psi was held on the system for

10 minutes. No leakage was observed through any specimens’ construction joint.

Decreases in water volume within the clear plastic tubing were recorded

immediately before air pressure was increased. All pressure systems other than the

system connected to the Synko-flex product leaked immediately. The pressure applied in

the previous experimental stage had caused leaks in the pressure systems that had not

been effectively repaired. Leakage occurred at the connection between the 6-inch PVC

cap and 6-inch pipe or at the interface between the pipe and flanged fitting. The Synko-

flex specimen was connected to a pressure system unused in stage one testing.

Leakage was experienced almost immediately in five of the six specimens. Water

volume changes were inaccurate for determining the effectiveness of different products at

preventing water penetration through a construction joint for the five specimens that

146

experienced pressure system leaks. The Synko-flex product was connected to the only

setup that contained no observable leaks from the pressure system.

Figure 9.3 shows a graph of the water volume decrease versus air pressure for the

Synko-flex specimen of stage two along with the MC-2010MN specimen and control

specimen with no construction joint of stage one. The three specimens have similar

water volume decreases with increases in air pressure even though stage two pressures

were increased more rapidly.

No leakage was observed through the construction joint of any specimen tested in

stage two. Volume decreases in stage two testing are similar to stage one testing for

specimens that experienced no leakage from the pressure system. All 10 specimens

tested in stages one and two should have had similar water volume decreases to those of

the control specimen without joint if no water losses occurred through the pressure

system. Water loss through leaks in the pressure system was the predominant factor

effecting water volume decreases.

147

Figure 9.3 - Water volume changes versus air pressure for the three specimens of

stages one and two that experienced no leakage from the pressure system.

0

1000

2000

3000

4000

5000

6000

0 20 40 60 80 100

Air Pressure (psi)

Volume (cm

3

)

Stage1_MC-2010MN Stage1_Control_NoJoint Stage2_Sykno-flex

148

Stage Three

The six specimens of stage three were constructed without mechanical vibration

of the concrete. The specimens were compacted by 10 stick-strikes of the slump rod per

specimen pour. The completed specimens contained significant honeycombing of the

concrete within the first few inches of each pour. No post-tensioning of the concrete was

performed. The six specimens tested included one control joint, the Tegraproof coating,

the mortar/slurry over normal initial pour, the Preco HI-V retarder to expose aggregate

along the joint, and two waterstops; MC-2010MN and Synko-flex.

Specimens were compacted without mechanical vibration and post-tensioning to

investigate the influence of compaction on leakage. The high occurrence of

honeycombing near the joint seemed likely to cause leakage through the construction

joints of the specimens, even at low pressures. Specimens were placed on their sides and

water was poured along the joint to determine whether specimens would leak without any

air pressure being applied.

Four of the six specimens completed in stage three constructions leaked

immediately when water was poured along the joint. Water leakage was fast enough to

ensure that placing the four specimens within the testing setup was meaningless because

water would leak at too high a rate to obtain meaningful results. The two specimens that

did not immediately leak were the mortar/slurry mixture over a normal initial pour and

the Tegraproof coating applied to the surface of the joint. The two specimens were

placed in the pressure system and water was added through the connection between the

galvanized pipe and clear plastic tubing. Water began leaking through the construction

joints within several minutes.

149

Leakage occurred through the two specimens within minutes due to their

prolonged exposure to the water added to the system. All six specimens initially had

water poured over the joint to check for leakage but only four leaked immediately. The

four specimens that immediately leaked had significant openings within the construction

joint that allowed a clear path for water flow through the joint. The mortar/slurry

specimen and Tegraproof specimen had smaller openings that caused water to take a less

direct path to penetrate through the specimens. The mortar/slurry helped improve

consolidation at the joint thereby limiting air voids at the joint and the Tegraproof coating

helped to cover the face of the joint thereby impeding waters path through the joint.

There was most likely a small hole that opened in the Tegraproof coating that allowed the

leak to occur.

Both specimens leaked through the construction joint before any air pressure was

added to the system. Water was continually added to the system until reaching the marks

drawn on the clear tubing four feet above the surface of the specimens at which point

measurements of water loss through the joint began being taken. Water that passed

through the construction joint of the two specimens was collected and weighed to

determine volume lost at varying times as shown in Figure 9.4. No pressure was applied

to the system until leakage had stopped for 35 minutes in one of the specimens.

An air pressure of 10psi was applied to the system after leakage had stopped for

35 minutes for the Tegraproof coated specimen. Pressures were increased 10psi every

hour for the remainder of the test. Testing was stopped after 30psi was held on the

system for one hour.

150

The Tegraproof and mortar/slurry mixture specimens had similar water leakage

amounts as shown in Figure 9.5. The graph shows total water lost immediately before air

pressures were increased. The Tegraproof product had less initial leakage when no air

pressure was on the system. The Tegraproof specimen healed itself more rapidly than the

slurry coating and was completely healed for 35 minutes before pressure was applied to

the system. When the 10psi air pressure was added the Tegraproof specimen quickly

began leaking more excessively than the mortar/slurry specimen. As pressure was

increased both the mortar/slurry and Tegraproof specimens leaked more excessively.

All six specimens tested in stage three leaked excessively before air pressure was

applied to the system. Four of the six specimens leaked when water was poured over the

construction joint. The two specimens that did not initially leak had either a surface

coating that helped prevent water penetration or contained a mortar/slurry at the joint that

improved consolidation at the joint. Both products leaked before any air pressure could

be applied to the system showing that compaction levels in the lab were inadequate to

allow the determination of the most effective product for limiting water penetration.

151

Figure 9.4 - Water volumes lost versus time for the stage three specimens tested.

0

500

1000

1500

2000

2500

3000

3500

4000

4500

0 50 100 150 200 250 300 350 400

Time (min)

Volume (cm

3

)

Mortar/slurry Tegraproof

152

Figure 9.5 - Total water volume lost at a given air pressure for stage three specimens

immediately before air pressure was increased.

0

500

1000

1500

2000

2500

3000

3500

4000

4500

0 5 10 15 20 25 30 35

Air Pressure (psi)

Total water volume lost (cm

3

)

Mortar/slurry-Normal Joint Tegraproof

153

8.4 THIRD EXPERIMENT: TEST RESULTS

The three waterstops tested in the third experiment performed very differently.

Measurements of waterstop expansion and thickness increases were taken. Waterstops

damaged during handling were removed from testing. Testing began with three samples

of each waterstop.

The Waterstop-RX 101TRH product swelled almost immediately when placed in

water. The Waterstop-RX products had expansion rates over 200 percent by day seven as

shown in Figure 9.6. The Waterstop-RX products became difficult to handle once soaked

and would easily break during handling. One sample was damaged after only one day of

testing. The other two Waterstop-RX 101TRH samples became too difficult to handle by

day seven.

The MC-2010MN product expanded much more slowly than the Waterstop-RX

product. The product had an expansion rate over 100% close to day 20 as shown in

Figure 9.7. The product was much easier to handle than the Waterstop-RX product.

After day 30 expansion of the product slowed considerably.

The Synko-flex product expanded the least. The product was not designed to

expand upon contact with water as test results showed. After 40 days of submersion in

water the Synko-flex product had expanded less than two percent as shown in Figure 9.8.

The average expansion rates of the three different waterstops are shown in Figure

9.9. The figure clearly shows that the Synko-flex product expands the least of any of the

three products while the Waterstop-RX product expanded the most. The average

thickness increases of the three waterstops are shown in Figure 9.10. The thickness

increases follow the general waterstop expansion rate increases.

154

0.00

50.00

100.00

150.00

200.00

250.00

0 1 2 3 4 5 6 7 8

Days

Expansion Rate %

Waterstop RX-1 Waterstop RX-2 Waterstop RX-3 Waterstop RX-AVG

Figure 9.6 - Expansion rates of Waterstop-RX 101TRH samples in the third

experiment.

155

Figure 9.7 - Expansion rates of MC-2010MN samples in the third experiment.

0.00

20.00

40.00

60.00

80.00

100.00

120.00

0 5 10 15 20 25 30 35 40 45

Days

Expansion Rate %

MC 2010MN-1 MC 2010MN-2 MC-2010MN-3 MC-2010MN-AVG

156

Figure 9.8 - Expansion rates of Synko-flex waterstop samples in the third

experiment.

0.00

0.20

0.40

0.60

0.80

1.00

1.20

1.40

1.60

1.80

2.00

0 5 10 15 20 25 30 35 40 45

Days

Expansion Rate %

Synko-Flex-1 Synko-Flex-2 Synko-Flex-3 Synko-Flex-AVG

157

Figure 9.9 - Average expansion rates of the three waterstops tested in the third

experiment.

0.00

50.00

100.00

150.00

200.00

250.00

0 5 10 15 20 25 30 35 40 45

Days

Expansion Rate %

Waterstop RX-AVG MC-2010MN_AVG Synko-Flex-AVG

158

Figure 9.10 - Average thickness increases of waterstop samples in the third

experiment.

0.00

5.00

10.00

15.00

20.00

25.00

30.00

0 5 10 15 20 25 30 35 40 45

Days

Thickness Increase (mm)

Waterstop-RX-AVG MC-2010MN_A V G Synko-Flex-A V G

159

CHAPTER 9: CONCLUSIONS AND RECOMMENDATIONS

9.1 CONCLUSIONS

The main objective of this study was to investigate alternatives for creating a

watertight construction joint for inclusion in the specifications for the Hood Canal East

Half Replacement Project. Determining the effectiveness of different products and

construction methods at preventing water penetration will give WSDOT a starting point

in building better more watertight joints for floating bridges.

The testing methods used in this study did not conform to a standard testing

method due to the lack of such methods. The first experiment performed in this study

worked correctly but the pressure applied by the system was too low to give any

significant experimental results. Consequently, a second experimental procedure was

used that applied a variable air pressure to the system. The system of the second

experiment did increase the pressure applied to the specimens by over five times the

pressure of experiment one but did not provide results for determining one products

effectiveness over another at preventing water penetration.

The first two experiments were effective in showing that compaction is the

deciding factor in water penetration through the construction joint. The greater the

concrete compaction at the joint the less likely it will leak under pressure. Specimens in

stages one and two were compacted to a higher level than stage three specimens through

the use of a mechanical stinger. There was excellent compaction at the joint and no

observed honeycombing in any of the specimens of the first two stages. Stage three

specimens were compacted by stick strikes of the slump rod dropped into the freshly

poured concrete. The compaction level of stage three specimens was much lower than

160

that of the first two stages. Honeycombing was observed in all specimens and was most

severe near the joint. The honeycombing provided openings within the concrete to easily

allow passage of water through the joint.

Product selection did not play an important role in preventing or decreasing water

leakage through the joint. Poorly compacted specimens leaked immediately regardless of

the applied product while all well-compacted specimens remained watertight.

Honeycombing of the concrete near the joint signified poor compaction that has a high

likelihood of leaking.

Products that should be most effective in helping to prevent water leakage through

the joint are those that increase compaction at the joint. The mortar/slurry mixture

applied to the first few inches of the joint helped improve compaction of the joint. The

stage three specimen built using this construction method was one of only two specimens

that did not leak before being placed within the testing setup. The removal of coarse

aggregate from the first few inches of the second pour allowed the concrete to compact at

a lower compaction effort than would be needed for a similar mix containing coarse

aggregate. The mortar/slurry had the added benefit of helping to replace fines lost from

segregation of the concrete when placed in a tall wall.

The third experiment was performed to determine the expansion rates of the three

waterstops submerged in water. The Waterstop-RX 101TRH and MC-2010MN products

saw significant expansion and thickness increases within the first two weeks of testing.

The use of these two products in a joint exposed to significant moisture for an extended

period of time could cause these products to lose their effectiveness as a water barrier.

The Synko-flex waterstop retained its original shape and should not be damaged by

161

extended exposure to significant moisture. The Synko-flex product performed the best of

the three waterstops tested in the third experiment but has not been proven to effectively

reduce water penetration at the joint; more testing needs to be performed using a

compaction level that demonstrates the Synko-Flex products ability to reduce water

penetration more effectively than a similar jointed control specimen for a given air

pressure.

9.2 GENERAL GUIDELINES FOR WATERTIGHT JOINT

The following general guidelines will help improve the resistance to water penetration for

a concrete construction joint.

1. The top surface of the joint should be compacted to as high a compaction level

as can be achieved in the field.

2. Repair any honeycombed concrete in the vicinity of the construction joint.

3. Use materials and construction methods to construct the joint that improve

compaction at the joint such as the mortar/slurry mixture.

4. Products such as waterstops and surface coatings may help to decrease water

penetration through the joint, but are far less important than good construction

practices when building the joint.

9.3 RECOMMENDATIONS FOR FURTHER STUDY

Clearly, there is a need for further testing to determine the ability of individual

products to prevent or reduce water penetration through a concrete construction joint.

162

The setup of the second experiment can be used to test these products. The products and

testing methods used in this study along with additional products should be tested using

the experimental setup of the second experiment with several small modifications.

The minimum compaction needed to prevent water leakage through the

construction joint of the control specimen should be determined for the initial 16.48psi

system pressure caused by the 4 foot water elevation. This minimum compaction should

be used with all specimens to determine the air pressure necessary to cause leakage

through the joint. Using this minimum compaction level will allow the most effective

products for limiting water penetration to be determined.

Additional tests should be performed on admixtures that improve concrete

compaction. The addition of these admixtures could limit water penetration through the

joint by improving compaction at the joint without an increase in labor. The use of

admixtures and other products that improve compaction should be studied further.

Testing should also be continued to determine the most effective surface

preparation for limiting water penetration at the joint. The raking method, exposed

aggregate surface and shear key should be further studied to determine the most effective

method for preventing water penetration. Test results were inconclusive in determining

the most effective surface preparation method for preventing water penetration;

additional testing is necessary.

All testing completed in this study was performed under static loading. Pontoons

in the field however are subjected to severe dynamic loading due to wind, wave and tidal

fluctuations. These dynamic forces could cause significant movement of the construction

joint that might lead to the formation of small cracks at the joint. Movement at the joint

163

could also cause damage to products applied to the joint. Testing should be performed to

apply dynamic forces to concrete specimens to study joint movement and subsequent

damage caused by this movement.

164

REFERENCES

Clear, C. A. (1985). “The Effects of Autogenous Healing Upon the Leakage of Water

Through Cracks in Concrete.” Technical Report-Cement and Concrete Association,

559(5).

Dusenberry, D. O., and DelloRusso, S. J. (1993). “Water Leakage Through Cracks in

Reinforced Concrete.” Proc., International Conference on Hydropower, 3(8), A. A.

Balkema, Rotterdam, Netherlands, 2167-2176.

Henley, E. H., Wilson, D. L., and Kolle, G. A. (1997). “ William A. Bugge Bridge

Replacement Plan for the East-Half Floating Portion.” Report, Washington State

Department of Transportation.

Kishel, J. (1989). “Seepage and Contraction Joints in Concrete Canal Linings.” Journal

of Irrigation and Drainage Engineering, 115(3), 377-382.

Liou, D. D. (1996). “The Effects of Construction Joint in Mass Concrete.” Materials for

the New Millenium. Proc. Fourth Materials Engineering Conference, 1(11), ASCE,

Washington DC, 193-202.

Lwin, M. M. (1993a). “The Lacey V. Murrow Floating Bridge, USA.” Structural

Engineering International, 145-148.

Lwin, M. M. (1993b). "Floating bridges-Solution to a difficult terrain." Transporation

Facilities through Difficult Terrain, J. T. H. Wu and R. K. Barrett, eds., Balkema,

Rotterdam, 581-591.

Lwin, M. M., Bruesch, A. W., and Evans, C. F. (1995). “High-Performance Concrete for

a Floating Bridge.” Fourth International Bridge Engineering Conference, National

Academy Press, Washington DC, 155-162.

Lwin, M. M., Dusenberry, D. O. (1994). “Responding to a floating bridge failure.” Public

Works, 125(1), 39-43.

Lwin, M. M. and Gloyd, G. S. (1984) “Rebuilding the Hood Canal Floating Bridge.”

Concrete International: Design and Construction, 6(6), 30-35.

Nichols, C. C. (1964). “Construction and Performance of Hood Canal Floating Bridge.”

Symposium on Concrete Construction in Aqueous Environment, ACI SP-8, 97-106.

Rashed, A., Rogowsky, D. M., and Elwi, A. E. (2000). “Tests on Reinforced Partially

Prestressed Concrete Tank Walls.” Journal of Structural Engineering, 126(6), 675-683.

165

Tan, K., and Gjorv, O. E. (1996). “Performance of Concrete Under Different Curing

Conditions.” Cement and Concrete Research, 26(3), 355-361.

Tatro, S. B., and Waring, S. T. (1988). “Waterstop Technology-The Next Chapter.”

Waterpower ’87, Proc., International Conference on Hydropower, 2, ASCE, New York,

1442-1451.

Wallis, S. (1992). “Putting Paid to Water Leakage Costs.” Tunnels and Tunnelling,

24(1), 51-54.

Wiss, Janney, Elstner Associates, Inc. (1993). “Concrete for Lacey V. Murrow Bridge

Pontoons.” Report, Washington State Department of Transportation, ed., Robert

LaFraugh.

WSDOT (2001). Standard Specifications for Road, Bridge and Municipal Construction

2002. Washington State Department of Transportation (WSDOT) Engineering

Publications, Olympia, WA.

Young, D.A., Munson, B.A., and Okiishi, T.H. (1997). A Brief Introduction to Fluid

Mechanics. John Wiley and Sons, Inc., New York, NY.

166

APPENDIX A

MEASURED MIX DATA

AND

STRAIN CALCULATIONS

167

Mix Design #1

LVM (Phase 1)

Mix # 1 - LVM Mix Design, Reference Mix

w/c ratio=

0.3291

mix proportions (per)

Concrete Constituent

1 yd

3

1.5 ft

3

Course Aggregate 1770 lb

98.35 lbs

Fine Aggregate 1295

71.95 lbs

Portland Cement Type II 624

34.65 lbs

Silica Fume (AASHTO M307) 50

2.8 lbs

Fly Ash (AASHTO M295) 100

5.55 lbs

Water (Total) 255

14.15 lbs

Water Reducer (ASTM C494)

none

Superplasticizer (ASTM C494) 5.5floz/cwt

70 mL



Slurry -

Silica fume = 2.8 lbs(all)

(1270.05grams)

Mix Water=total-slurry water

Water = 3.42lbs

(1551.28grams)

=

10.73 lbs

HRWR = 6mL

168

Concrete for Hood Canal Floating Bridge Replacement Project

Concrete Mix Design -

LVM Mix Design, Reference Mix

Mix Design # - 1

Date Batched and Specimens Cast - November 14, 2002

Slump - 8.0"

Air Content - -

Batch Temperature - 66 F

Number of specimens cast (6x12 and 4x8) - 7 and 2 (#'s 1-9)

Date drilled and fitted with gage points - December 10, 2002

28-day Curing Date - December 12 (13), 2002

28-day Compressive Strength - Break notes

Cylinder f'c-1 =

8910

psi (252,170 lbs) 2 cones

Cylinder f'c-2 =

8650

psi (244,730 lbs) Cone/Shear

Cylinder f'c-3 =

8570

psi (242,480 lbs) Cone/Shear

Average =

8710

psi

Load to Apply for Creep Test - ASTM C 512

= 40% x f'c (28 day)

=.40 x 8710 psi = 3484 psi

Actual Applied Load =

30 tons = 24.4 % f'c (28 day) = 2122psi

Creep and Shrinkage Measurements

Cylinder C-1 (mix #_____) Cylinder C-2 (mix #_____)

Actual date Creep Measurement Creep Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading1/14 3:00pm 0.1649 0.1617 0.1592 0.1606 0.1561 0.1406

Immediately after Loading1/14 3:53p 0.1615 0.1581 0.1554 0.1571 0.1529 0.137

15-20 minutes1/14 4:20p 0.1614 0.1577 0.1551 0.156 0.1517 0.1362

1 hour1/14 5:06p 0.1605 0.1569 0.1541 0.1553 0.1512 0.1364

2 hours: 45 minutes1/14 6:45p 0.1603 0.1563 0.1541 0.1549 0.1503 0.1352

6 - 8 hours1/14 9:56p 0.1602 0.1559 0.155 0.1541 0.1497 0.1354

2nd Day1/15 1:50p 0.1597 0.1554 0.1548 0.1539 0.1494 0.1349

3rd Day1/16 11:35a 0.1596 0.1549 0.1535 0.1533 0.1492 0.135

4th Day1/17 1:40p 0.1589 0.1544 0.1535 0.153 0.1491 0.1348

6th Day1/19 12:15p 0.1579 0.1541 0.153 0.1525 0.1486 0.1341

8th Day1/21 1:35p 0.1573 0.1537 0.1526 0.1522 0.1485 0.1339

9th Day1/22 1:52p 0.157 0.1535 0.1518 0.1519 0.1482 0.1337

14th Day1/28 3:30p 0.1565 0.1532 0.1516 0.1516 0.1479 0.1335

21st Day2/4 4:30p 0.156 0.1529 0.1513 0.1514 0.1474 0.1332

28th day2/11 4:10p 0.1558 0.1527 0.1509 0.151 0.1469 0.1329

recovery2/11 4:11p 0.159 0.1553 0.1538 0.1538 0.1495 0.1346

169

Creep and Shrinkage Measurements (Continued)

Cylinder S-1 (mix #_____) Cylinder S-2 (mix #_____)

Actual date Shrinkage Measurement Shrinkage Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading1/14 3:00pm 0.1536 0.1305 0.1228 0.1575 0.1429

Immediately after Loading1/14 3:53p 0.1536 0.1305 0.1225 0.1575 0.1427

15-20 minutes1/14 4:20p 0.1535 Gage 0.1302 0.1225 0.1572 0.1427

1 hour1/14 5:06p 0.1535 0.1292 0.1225 0.1573 0.1428

2 hours: 45 minutes1/14 6:45p 0.1534 0.1301 0.1227 0.1572 0.1429

6 - 8 hours1/14 9:56p 0.1534 Length 0.1304 0.1227 0.158 0.1426

2nd Day1/15 1:50p 0.1534 0.1297 0.1226 0.1579 0.1424

3rd Day1/16 11:35a 0.1532 0.1306 0.1224 0.1577 0.1427

4th Day1/17 1:40p 0.1534 Not 0.1304 0.1224 0.158 0.1422

6th Day1/19 12:15p 0.1533 0.1302 0.1224 0.158 0.1422

8th Day1/21 1:35p 0.1532 0.1301 0.1223 0.1575 0.1418

9th Day1/22 1:52p 0.153 Good 0.1303 0.122 0.1574 0.1416

14th Day1/28 3:30p 0.1529 0.1299 0.1218 0.1573 0.1415

21st Day2/4 4:30p 0.1528 0.1294 0.1218 0.1571 0.1415

28th day2/11 4:10p 0.1528 0.1293 0.1218 0.1571 0.1415

recovery2/11 4:11p 0.1528 0.1293 0.1218 0.1571 0.1415

170

Mix Design #1 - LVM Mix Design

Creep Measurements



gage zero (10") = 0.1600



T

i



0



0

.

0

.

0

.

0

.

0

.

0

.

1

.

2

.

4

.

6

.

7

.

1

4

1

3

2

1

2

0

2

8

2

7

r

e

2

7



Shrinkage Measurements



gage zero (10") = 0.1600



T

i



0



0

.

0

.

0

.

0

.

0

.

0

.

1

.

2

.

4

.

6

.

7

.

1

4

1

3

2

1

2

0

2

8

2

7

r

e

2

7

171

(Creep)

average average Average total

Cylinder #6 total total Strain - 2

Cylinder plane # strain strain Cylinders

1 2 3 (in) (in/in) (in)

0.1606 10.0006 0.1561 9.9961 0.1406 9.9806

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0035 0.00035 0.0032 0.00032 0.0036 0.00036 0.0034 0.00034 0.0035

0.0046 0.00046 0.0044 0.00044 0.0044 0.00044 0.0045 0.00045 0.0042

0.0053 0.00053 0.0049 0.00049 0.0042 0.00042 0.0048 0.00048 0.0048

0.0057 0.00057 0.0058 0.00058 0.0054 0.00054 0.0056 0.00056 0.0053

0.0065 0.00065 0.0064 0.00064 0.0052 0.00052 0.0060 0.00060 0.0055

0.0067 0.00067 0.0067 0.00067 0.0057 0.00057 0.0064 0.00064 0.0058

0.0073 0.00073 0.0069 0.00069 0.0056 0.00056 0.0066 0.00066 0.0063

0.0076 0.00076 0.0070 0.00070 0.0058 0.00058 0.0068 0.00068 0.0066

0.0081 0.00081 0.0075 0.00075 0.0065 0.00065 0.0074 0.00074 0.0072

0.0084 0.00084 0.0076 0.00076 0.0067 0.00067 0.0076 0.00076 0.0075

0.0087 0.00087 0.0079 0.00079 0.0069 0.00069 0.0078 0.00078 0.0078

0.0090 0.00090 0.0082 0.00082 0.0071 0.00071 0.0081 0.00081 0.0081

0.0092 0.00092 0.0087 0.00087 0.0074 0.00074 0.0084 0.00084 0.0085

0.0096 0.00096 0.0092 0.00092 0.0077 0.00077 0.0088 0.00088 0.0088

0.0068 0.00068 0.0066 0.00066 0.0060 0.00060 0.0065 0.00065 0.0062

(Shrinkage)

average Average Shrinkage

Cylinder #7 average shrinkage Strain - 2

Cylinder plane shrinkage strain Cylinders

1 2 3 strain (in/in) (in)

0.1228 9.9628 0.1575 9.9975 0.1429 9.9829

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0003 0.00003 0.0000 0.00000 0.0002 0.00002 0.0002 0.00002 0.0001

0.0003 0.00003 0.0003 0.00003 0.0002 0.00002 0.0003 0.00003 0.0002

0.0003 0.00003 0.0002 0.00002 0.0001 0.00001 0.0002 0.00002 0.0004

0.0001 0.00001 0.0003 0.00003 0.0000 0.00000 0.0001 0.00001 0.0002

0.0001 0.00001 -0.0005 -0.00005 0.0003 0.00003 0.0000 0.00000 0.0001

0.0002 0.00002 -0.0004 -0.00004 0.0005 0.00005 0.0001 0.00001 0.0003

0.0004 0.00004 -0.0002 -0.00002 0.0002 0.00002 0.0001 0.00001 0.0001

0.0004 0.00004 -0.0005 -0.00005 0.0007 0.00007 0.0002 0.00002 0.0002

0.0004 0.00004 -0.0005 -0.00005 0.0007 0.00007 0.0002 0.00002 0.0003

0.0005 0.00005 0.0000 0.00000 0.0011 0.00011 0.0005 0.00005 0.0005

0.0008 0.00008 0.0001 0.00001 0.0013 0.00013 0.0007 0.00007 0.0006

0.0010 0.00010 0.0002 0.00002 0.0014 0.00014 0.0009 0.00009 0.0008

0.0010 0.00010 0.0004 0.00004 0.0014 0.00014 0.0009 0.00009 0.0009

0.0010 0.00010 0.0004 0.00004 0.0014 0.00014 0.0009 0.00009 0.0010

172

Average total

Strain - 2

Cylinders (microstrain)

Time,m Time, day

(in/in)

(x 10^6)

0 0

0

53 0.0

0.000351768

351.8

80 0.1

0.000416799

416.8

126 0.1

0.000478453

478.5

225 0.2

0.000533494

533.5

416 0.3

0.000546821

546.8

1335 0.9

0.0005835

583.5

2670 1.9

0.000626831

626.8

4115 2.9

0.00065683

656.8

6910 4.8

0.000715181

715.2

9790 6.8

0.000748516

748.5

11247 7.8

0.000783522

783.5

18720 13.0

0.000813525

813.5

28800 20.0

0.000848533

848.5

38880 27.0

0.000881878

881.9

38881 27.0

0.000618505

618.5

Shrinkage Measurements

Creep= Creep=

Average Shrinkage

Total

Strain - 2

minus

Cylinders

(microstrain) Shrinkage

Shrinkage

(microstrain)

Time,m Time, day

(in/in)

(x 10^6) (in)

(in/in)

(x 10^6)

0 0

0

0 0.0000

0.000000

0

53 0.0

8.33951E-06

8.3 0.0034

0.000343

343.4

80 0.1

2.33408E-05

23.3 0.0039

0.000393

393.5

126 0.1

4.50056E-05

45.0 0.0043

0.000433

433.4

225 0.2

2.16669E-05

21.7 0.0051

0.000512

511.8

416 0.3

5.83745E-06

5.8 0.0054

0.000541

541.0

1335 0.9

3.00125E-05

30.0 0.0055

0.000553

553.5

2670 1.9

1.41663E-05

14.2 0.0061

0.000613

612.7

4115 2.9

1.75168E-05

17.5 0.0064

0.000639

639.3

6910 4.8

2.5016E-05

25.0 0.0069

0.000690

690.2

9790 6.8

4.66977E-05

46.7 0.0070

0.000702

701.8

11247 7.8

5.67017E-05

56.7 0.0073

0.000727

726.8

18720 13.0

7.58716E-05

75.9 0.0074

0.000738

737.7

28800 20.0

9.4206E-05

94.2 0.0075

0.000754

754.3

38880 27.0

9.67062E-05

96.7 0.0079

0.000785

785.2

38881 27.0

9.67062E-05

96.7 0.0052

0.000522

521.8

173

Mix #1

LVM Mix Design, Reference Mix (Phase 1)

Applied Creep Load =

2120

psi Specific

Creep Specific Specific

Time Total Creep Shrinkage plus Initial Creep Total

(min) (in/in) (in/in) (in/in) (microstrain/psi)

(microstrain/psi)

0 0 0 0 0 0

53 .352E-3 .343E-3 .834E-5 0.162 0 0.166

80 .417E-3 .393E-3 .233E-4 0.186 0.024 0.197

126 .478E-3 .433E-3 .450E-4 0.204 0.042 0.226

225 .533E-3 .512E-3 .217E-4 0.241 0.079 0.252

416 .547E-3 .541E-3 .584E-5 0.255 0.093 0.258

1335 .584E-3 .553E-3 .300E-4 0.261 0.099 0.275

2670 .627E-3 .613E-3 .142E-4 0.289 0.127 0.296

4115 .657E-3 .639E-3 .175E-4 0.302 0.140 0.310

6910 .715E-3 .690E-3 .250E-4 0.326 0.164 0.337

9790 .749E-3 .702E-3 .467E-4 0.331 0.169 0.353

11247 .784E-3 .727E-3 .567E-4 0.343 0.181 0.370

18720 .814E-3 .738E-3 .759E-4 0.348 0.186 0.384

28800 .849E-3 .754E-3 .942E-4 0.356 0.194 0.400

.

38881 .619E-3 .522E-3 .967E-4 0.246 0.292

174

Mix Design #2

WJE, Inc Report Recommendation

Mix # 2 - 1st Alteration - WJE, Inc. Report Recommendation w/c ratio=

0.3287

mix proportions (per)

Concrete Constituent

1 yd

3

1.5 ft

3

Course Aggregate 1770 lb 98.35 lbs

Fine Aggregate 1295 71.95 lbs

Portland Cement Type II 540 30 lbs

Silica Fume (AASHTO M307) 35 1.95 lbs

Fly Ash (AASHTO M295) 200 11.1 lbs

Water

255 14.15 lbs

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 4.3floz/cwt 55 mL



Slurry - Silica fume=1.95lbs(all)

(884.5grams) Mix Water=total-slurry water

Water=2.38lbs (1079.5grams) =

11.77

lbs

HRWR=6mL

175

Concrete for Hood Canal Floating Bridge Replacement Project

Concrete Mix Design -

WJE, Inc Report Recommendation

Mix Design # 2

Date Batched and Specimens Cast - November 14, 2002

Slump - 7.5 "

Air Content - -

Batch Temperature - 66 F

Number of specimens cast (6x12 and 4x8) - 7 and 2 (#'s 10 - 18)

Date drilled and fitted with gage points - December 10, 2002

28-day Curing Date - December 12 (13), 2002

28-day Compressive Strength - Break notes

Cylinder f'c-1 = 8140psi (230360 lbs) 2 cones

Cylinder f'c-2 = 8200psi (232130 lbs) 2 cones

Cylinder f'c-3 = 8150psi (230790 lbs) 2 cones

Average =

8163.3psi

Load to Apply for Creep Test - ASTM C 512

= 40% x f'c (28 day)

=.40 x 8163.3 psi = 3265.3 psi

Actual Applied Load =

28.1 tons psi = 24.4% f'c (28 day) = 1988 psi

Creep and Shrinkage Measurements

#13 #14

Cylinder C-1 (mix #_____) Cylinder C-2 (mix #_____)

Actual date Creep Measurement Creep Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading1/14 4:35pm 0.1545 0.1561 0.1599 0.163 0.157 0.154

Immediately after Loading1/14 5:00p 0.1514 0.1544 0.1564 0.1611 0.1543 0.1519

15-20 minutes1/14 5:20p 0.1477 0.1532 0.1565 0.1595 0.1544 0.1495

1 hour1/14 6:07p 0.1474 0.152 0.1539 0.1593 0.1542 0.1485

2 hours: 45 minutes1/14 7:59p 0.1478 0.1525 0.1542 0.16 0.155 0.149

6 - 8 hours1/14 11:00p 0.1479 0.1525 0.1531 0.1593 0.155 0.149

2nd Day1/15 1:53p 0.1466 0.1515 0.1528 0.1588 0.1551 0.1479

3rd Day1/16 11:45a 0.147 0.1515 0.1525 0.1587 0.1548 0.1478

4th Day1/17 1:51p 0.1466 0.1515 0.1523 0.1585 0.1547 0.1474

6th Day1/19 12:30p 0.1459 0.1511 0.1519 0.1581 0.1541 0.1471

8th Day1/21 1:40p 0.1456 0.1506 0.1516 0.1576 0.154 0.1468

9th Day1/22 5:00p 0.1452 0.1502 0.1514 0.1572 0.1538 0.1464

14th Day1/28 3:40p 0.1445 0.1499 0.1507 0.1566 0.1533 0.1456

21st Day2/4 4:40p 0.1443 0.1496 0.1503 0.1563 0.1531 0.1454

28th day2/11 4:15p 0.1441 0.1493 0.15 0.1561 0.153 0.1451

recovery2/11 4:16p 0.1475 0.1522 0.1535 0.1595 0.1558 0.1491

176

Creep and Shrinkage Measurements (Continued)

Cylinder S-1 (mix #_____) Cylinder S-2 (mix #_____)

Actual date Shrinkage Measurement Shrinkage Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading1/14 4:35pm 0.1506 0.1415 0.1421 0.1615 0.154

Immediately after Loading1/14 5:00p 0.15 0.1415 0.142 0.1615 0.1542

15-20 minutes1/14 5:20p 0.1491 Gage 0.1413 0.1421 0.1605 0.154

1 hour1/14 6:07p 0.148 0.1397 0.1398 0.1595 0.1529

2 hours: 45 minutes1/14 7:59p 0.149 0.1403 0.1402 0.1596 0.1524

6 - 8 hours1/14 11:00p 0.1486 Length 0.1403 0.1396 0.1597 0.1524

2nd Day1/15 1:53p 0.1481 0.1398 0.1396 0.1595 0.1522

3rd Day1/16 11:45a 0.148 0.1397 0.1395 0.1594 0.1521

4th Day1/17 1:51p 0.1481 Not 0.1396 0.14 0.1594 0.1522

6th Day1/19 12:30p 0.1478 0.1394 0.1385 0.1593 0.1518

8th Day1/21 1:40p 0.1476 0.1393 0.1395 0.1592 0.1517

9th Day1/22 5:00p 0.1474 Good 0.1391 0.1394 0.1591 0.1517

14th Day1/28 3:40p 0.148 0.1392 0.1393 0.1591 0.1516

21st Day2/4 4:40p 0.1476 0.139 0.139 0.1588 0.1515

28th day2/11 4:15p 0.1474 0.1388 0.1389 0.1587 0.1515

recovery2/11 4:16p 0.1474 0.1388 0.1389 0.1587 0.1515

177

Mix # 2 - WJE, Inc Report Recommendation

Creep Measurements



gage zero (10") = 0.1600



Cylinder # 13 average total

Cylinder plane total strain

T

i



0



0

.

0

.

0

.

0

.

0

.

0

.

1

.

2

.

4

.

6

.

7

.

1

4

1

3

2

1

2

0

2

8

2

7

r

e

2

7



Shrinkage Measurements

gage zero (10") =

0.1600

average

Cylinder #15 average shrinkage

Cylinder plane shrinkage strain

T

i



0



25 0.0 0.0006 0.0001 Gage 0.0000 0.0000 0.0003 0.000030

0

.

0

.

199 0.1 0.0016 0.0002 Length 0.0012 0.0001 0.0014 0.000140

0

.

0

.

2585 1.8 0.0026 0.0003 Not 0.0018 0.0002 0.0022 0.000220

2

.

4

.

9780 6.8 0.0030 0.0003 Good 0.0022 0.0002 0.0026 0.000260

7

.

1

4

1

3

2

1

2

0

2

7

r

e

2

7

178

(Creep)

average

Cylinder # 14 average total

Average total

Cylinder plane total strain

Strain - 2

1 2 3 strain (in/in)

Cylinders

0.163 10.0030 0.157 9.9970 0.154

9.9940

0.0000 0.0000 0.0000 0.0000 0.0000

0.0000

0.0000 0.00000

0.0000

0.0019 0.0002 0.0027 0.0003 0.0021

0.0002

0.0022 0.00022

0.0025

0.0035 0.0003 0.0026 0.0003 0.0045

0.0005

0.0035 0.00035

0.0040

0.0037 0.0004 0.0028 0.0003 0.0055

0.0006

0.0040 0.00040

0.0049

0.0030 0.0003 0.0020 0.0002 0.0050

0.0005

0.0033 0.00033

0.0043

0.0037 0.0004 0.0020 0.0002 0.0050 0

.0005

0.0036 0.00036

0.0046

0.0042 0.0004 0.0019 0.0002 0.0061

0.0006

0.0041 0.00041

0.0053

0.0043 0.0004 0.0022 0.0002 0.0062

0.0006

0.0042 0.00042

0.0054

0.0045 0.0004 0.0023 0.0002 0.0066

0.0007

0.0045 0.00045

0.0056

0.0049 0.0005 0.0029 0.0003 0.0069

0.0007

0.0049 0.00049

0.0060

0.0054 0.0005 0.0030 0.0003 0.0072

0.0007

0.0052 0.00052

0.0064

0.0058 0.0006 0.0032 0.0003 0.0076

0.0008

0.0055 0.00055

0.0067

0.0064 0.0006 0.0037 0.0004 0.0084

0.0008

0.0062 0.00062

0.0073

0.0067 0.0007 0.0039 0.0004 0.0086

0.0009

0.0064 0.00064

0.0076

0.0069 0.0007 0.0040 0.0004 0.0089

0.0009

0.0066 0.00066

0.0078

0.0035 0.0003 0.0012 0.0001 0.0049

0.0005

0.0032 0.00032

0.0045

(Shrinkage)

average

Cylinder #16

average shrinkage

Average Shrinkage

Cylinder plane

shrinkage strain

Strain - 2

1 2 3 strain (in/in)

Cylinders

0.1421 9.9821 0.1615 10.0015 0.154 9.9940

0.0000 0.0000 0.0000 0.0000 0.0000 0.0000 0.0000 0.00000

0.0000

0.0001 0.0000 0.0000 0.0000 -0.0002 0.0000 0.0000 0.00000

0.0001

0.0000 0.0000 0.0010 0.0001 0.0000 0.0000 0.0003 0.00003

0.0006

0.0023 0.0002 0.0020 0.0002 0.0011 0.0001 0.0018 0.00018

0.0020

0.0019 0.0002 0.0019 0.0002 0.0016 0.0002 0.0018 0.00018

0.0016

0.0025 0.0003 0.0018 0.0002 0.0016 0.0002 0.0020 0.00020

0.0018

0.0025 0.0003 0.0020 0.0002 0.0018 0.0002 0.0021 0.00021

0.0021

0.0026 0.0003 0.0021 0.0002 0.0019 0.0002 0.0022 0.00022

0.0022

0.0021 0.0002 0.0021 0.0002 0.0018 0.0002 0.0020 0.00020

0.0021

0.0036 0.0004 0.0022 0.0002 0.0022 0.0002 0.0027 0.00027

0.0026

0.0026 0.0003 0.0023 0.0002 0.0023 0.0002 0.0024 0.00024

0.0025

0.0027 0.0003 0.0024 0.0002 0.0023 0.0002 0.0025 0.00025

0.0026

0.0028 0.0003 0.0024 0.0002 0.0024 0.0002 0.0025 0.00025

0.0025

0.0031 0.0003 0.0027 0.0003 0.0025 0.0003 0.0028 0.00028

0.0028

0.0032 0.0003 0.0028 0.0003 0.0025 0.0003 0.0028 0.00028

0.0029

0.0032 0.0003 0.0028 0.0003 0.0025 0.0003 0.0028 0.00028

0.0029

179

Average total

Strain - 2

Cylinders

Time,m Time, day

(in/in)

(x 10^6)

0 0

0

25 0.0

0.000250065

250.0651

40 0.0

0.000395122

395.1223

87 0.1

0.00048681

486.81

199 0.1

0.000433464

433.4642

380 0.3

0.000461793

461.7933

1273 0.9

0.000530153

530.1531

2585 1.8

0.000536818

536.8181

4151 2.9

0.000558492

558.492

6890 4.8

0.000605172

605.1718

9780 6.8

0.000638512

638.5122

11420 7.9

0.000671855

671.8548

18720 13.0

0.000731871

731.8708

28800 20.0

0.000758543

758.5428

38880 27.0

0.000781882

781.8825

38881 27.0

0.000448461

448.4615

Creep=

Average Shrinkage

Creep=

Total

Strain - 2

Total

minus

Cylinders

minus

Shrinkage

Time,m Time, day

(in/in)

(x 10^6) Shrinkage

(in/in)

(x 10^6)

0 0

0

0 0.0000

0

25 0.0

1.33484E-05

13.34843 0.0024

0.0002367

236.7167

40 0.0

5.92087E-05

59.20872 0.0034

0.0003359

335.9136

87 0.1

0.000200219

200.2193 0.0029

0.0002866

286.5907

199 0.1

0.000160161

160.1613 0.0027

0.0002733

273.3029

380 0.3

0.000178522

178.5222 0.0028

0.0002833

283.2711

1273 0.9

0.000210225

210.2253 0.0032

0.0003199

319.9278

2585 1.8

0.000220236

220.236 0.0032

0.0003166

316.5821

4151 2.9

0.000210222

210.2224 0.0035

0.0003483

348.2697

6890 4.8

0.000256121

256.1206 0.0035

0.0003491

349.0512

9780 6.8

0.000250267

250.2675 0.0039

0.0003882

388.2447

11420 7.9

0.000263618

263.6175 0.0041

0.0004082

408.2373

18720 13.0

0.000249436

249.4361 0.0048

0.0004824

482.4347

28800 20.0

0.000276131

276.1307 0.0048

0.0004824

482.4122

38880 27.0

0.000289481

289.4807 0.0049

0.0004924

492.4018

38881 27.0

0.000289481

289.4807 0.0016

0.000159

158.9808

180

Mix #2

WJE, Inc Report Recommendation

Applied Creep Load =

1990psi Specific

Creep Specific Specific

Time Total Creep Shrinkage plus Initial Creep Total

(min) (in/in) (in/in) (in/in) (microstrain/psi)

(microstrain/psi)

0 0 0 0 0 0

25 .250E-3 .237E-3

.133E-4 0.119 0 0.126

40 .395E-3 .336E-3

.592E-4 0.169 0.050 0.199

87 .487E-3 .287E-3

.200E-3 0.144 0.025 0.245

199 .433E-3 .273E-3

.160E-3 0.137 0.018 0.218

380 .462E-3 .283E-3

.179E-3 0.142 0.023 0.232

1273 .530E-3 .320E-3

.210E-3 0.161 0.042 0.266

2585 .537E-3 .317E-3

.220E-3 0.159 0.040 0.270

4151 .558E-3 .348E-3

.210E-3 0.175 0.056 0.281

6890 .605E-3 .349E-3

.256E-3 0.175 0.056 0.304

9780 .639E-3 .388E-3

.250E-3 0.195 0.076 0.321

11420 .672E-3 .408E-3

.264E-3 0.205 0.086 0.338

18720 .732E-3 .482E-3

.249E-3 0.242 0.123 0.368

28800 .759E-3 .482E-3

.276E-3 0.242 0.123 0.381

.

38881 .448E-3 .159E-3

.289E-3 0.080 0.225

181

Mix Design #3

Metakaolin 5% OPC Replacement

Mix # 3 - 2nd Alteration - Metakaolin - 5% OPC Replacement* w/c ratio=

0.3287

mix proportions (per)

Concrete Constituent

1 yd

3

1.5 ft

3

Course Aggregate 1770 lb 98.35 lbs

Fine Aggregate 1295 71.95 lbs

Portland Cement Type II 636.3 35.35 lbs

Silica Fume (AASHTO M307)

none none

Fly Ash (AASHTO M295) 100 5.55 lbs-------->

2517.4g

Metakaolin (High Reactive) 38.75 2.15 lbs-------->

975.2g

Water

255 14.15 lbs

Water Reducer (ASTM C494)

none

Superplasticizer (ASTM C494)

5.5floz/cwt 70 mL

* Based on 775 pounds of total cementitious materials

182

Concrete for Hood Canal Floating Bridge Replacement Project

Concrete Mix Design -

Metakaolin - 5% OPC Replacement

Mix Design # 3

Date Batched and Specimens Cast - November 14, 2002

Slump - 9 "

Air Content - -

Batch Temperature - 66 F

Number of specimens cast (6x12 and 4x8) - 7 and 2 (#'s 19 - 27)

Date drilled and fitted with gage points - December 10, 2002

28-day Curing Date - December 12 (13), 2002

28-day Compressive Strength - Break notes

Cylinder f'c-1 =

8820

psi (249700 lbs) 2 cones

Cylinder f'c-2 =

8780

psi (248370 lbs) Shear Plane

Cylinder f'c-3 =

8720

psi (246800 lbs) 2 cones

Average =

8773.3

psi

Load to Apply for Creep Test - ASTM C 512

= 40% x f'c (28 day)

=.40 x 8773.3 psi = 3509.3 psi

Actual Applied Load =

30.3 tons = 24.4% f'c (28 day) = 2140.7 psi

Creep and Shrinkage Measurements

#23 #24

Cylinder C-1 (mix #_____) Cylinder C-2 (mix #_____)

Actual date Creep Measurement Creep Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading

1/14 5:37pm 0.1578 0.1501 0.1307 0.17 0.1635 0.1923

Immediately after Loading

1/14 6:01p 0.1551 0.1473 0.1279 0.1666 0.1603 0.1898

15-20 minutes

1/14 6:18p 0.155 0.147 0.1275 0.166 0.1599 0.1891

1 hour

1/14 7:00p 0.155 0.1467 0.1274 0.1657 0.1594 0.1876

2 hours: 45 minutes

1/14 8:45p 0.1555 0.1465 0.1279 0.1658 0.1594 0.1879

6 - 8 hours

1/14 12:01am 0.1559 0.1469 0.1279 0.1658 0.1594 0.1877

2nd Day

1/15 2:04p 0.1548 0.146 0.1264 0.1645 0.159 0.1868

3rd Day

1/16 11:51a 0.1543 0.1459 0.1255 0.1646 0.1582 0.1866

4th Day

1/17 1:55p 0.1539 0.145 0.1256 0.1643 0.1582 0.1865

6th Day

1/19 12:35p 0.1535 0.1443 0.1253 0.1638 0.1578 0.1861

8th Day

1/21 1:50p 0.1533 0.1435 0.1249 0.1634 0.1576 0.1855

9th Day

1/22 5:05p 0.1526 0.1433 0.1245 0.1632 0.157 0.1852

14th Day

1/28 4:00p 0.152 0.1428 0.1237 0.163 0.1566 0.1845

21st Day

2/4 4:45p 0.1512 0.1424 0.1234 0.1625 0.1564 0.1842

28th day

2/11 4:00p 0.1505 0.1422 0.1232 0.1623 0.1562 0.184

recovery

2/11 4:01p 0.1534 0.1456 0.1268 0.1649 0.1586 0.1879

183

#22 #25

Cylinder S-1 (mix #_____) Cylinder S-2 (mix #_____)

Actual date Shrinkage Measurement Shrinkage Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading

1/14 5:37pm 0.1655 0.0705 0.164 0.159 0.0641 0.12

Immediately after Loading

1/14 6:01p 0.1653 0.0704 0.1638 0.1593 0.064 0.12

15-20 minutes

1/14 6:18p 0.165 0.07 0.1636 0.1585 0.0653 0.119

1 hour

1/14 7:00p 0.1654 0.0708 0.164 0.1581 0.0649 0.1191

2 hours: 45 minutes

1/14 8:45p 0.1651 0.0705 0.1641 0.1591 0.0636 0.12

6 - 8 hours

1/14 12:01am 0.165 0.0706 0.164 0.1586 0.063 0.12

2nd Day

1/15 2:04p 0.1649 0.07 0.1636 0.1581 0.0628 0.12

3rd Day

1/16 11:51a 0.1646 0.07 0.164 0.158 0.063 0.1195

4th Day

1/17 1:55p 0.165 0.0701 0.1641 0.1576 0.0628 0.1195

6th Day

1/19 12:35p 0.1646 0.07 0.1636 0.1574 0.0628 0.1195

8th Day

1/21 1:50p 0.1645 0.0695 0.1633 0.1568 0.0625 0.1193

9th Day

1/22 5:05p 0.1645 0.0693 0.1632 0.1568 0.0625 0.1193

14th Day

1/28 4:00p 0.1646 0.0695 0.1636 0.157 0.0625 0.1194

21st Day

2/4 4:45p 0.1644 0.0693 0.1634 0.1569 0.0625 0.119

28th day

2/11 4:00p 0.1643 0.0693 0.1631 0.1568 0.0625 0.119

recovery

2/11 4:01p 0.1643 0.0693 0.1631 0.1568 0.0625 0.119

184

Mix # 3 - Metakaolin - 5% OPC Replacement

Creep Measurements



gage zero (10") = 0.1600



Cylinder # 23 average total

Cylinder plane total strain

T

i



0



0

.

0

.

0

.

0

.

0

.

0

.

1

.

2

.

4

.

6

.

8

.

1

4

1

3

2

1

2

0

2

8

2

7

r

e

2

7



Shrinkage Measurements

gage zero (10") = 0.1600 average

Cylinder # 22 average shrinkage

Cylinder plane shrinkage strain

T

i



0



0

.

0

.

0

.

0

.

0

.

0

.

1

.

2

.

4

.

6

.

8

.

1

4

1

3

2

1

2

0

2

8

2

7

r

e

2

7

185

(creep)

average

Cylinder # 24 average total Average total

Cylinder plane total strain Strain - 2

1

2

3 strain (in/in) Cylinders

0.17 10.0100 0.1635 10.0035 0.1923 10.0323

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0034 0.00034 0.0032 0.00032 0.0025 0.00025 0.0030 0.00030 0.0029

0.0040 0.00040 0.0036 0.00036 0.0032 0.00032 0.0036 0.00036 0.0033

0.0043 0.00043 0.0041 0.00041 0.0047 0.00047 0.0044 0.00044 0.0038

0.0042 0.00042 0.0041 0.00041 0.0044 0.00044 0.0042 0.00042 0.0036

0.0042 0.00042 0.0041 0.00041 0.0046 0.00046 0.0043 0.00043 0.0035

0.0055 0.00055 0.0045 0.00045 0.0055 0.00055 0.0052 0.00052 0.0045

0.0054 0.00054 0.0053 0.00053 0.0057 0.00057 0.0055 0.00055 0.0049

0.0057 0.00057 0.0053 0.00053 0.0058 0.00058 0.0056 0.00056 0.0052

0.0062 0.00062 0.0057 0.00057 0.0062 0.00062 0.0060 0.00060 0.0056

0.0066 0.00066 0.0059 0.00059 0.0068 0.00068 0.0064 0.00064 0.0060

0.0068 0.00068 0.0065 0.00065 0.0071 0.00071 0.0068 0.00068 0.0064

0.0070 0.00070 0.0069 0.00069 0.0078 0.00078 0.0072 0.00072 0.0070

0.0075 0.00075 0.0071 0.00071 0.0081 0.00081 0.0076 0.00076 0.0074

0.0077 0.00077 0.0073 0.00073 0.0083 0.00083 0.0078 0.00078 0.0077

0.0051 0.00051 0.0049 0.00049 0.0044 0.00044 0.0048 0.00048 0.0045

(shrinkage)

average Average Shrinkage

Cylinder # 25 average shrinkage Strain - 2

Cylinder plane shrinkage strain Cylinders

1

2

3 strain (in/in) (in)

0.159 9.9990 0.0641 9.9041 0.12 9.9600

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

-0.0003 -0.00003 0.0001 0.00001 0.0000 0.00000 -0.0001 -0.00001 0.0001

0.0005 0.00005 -0.0012 -0.00012 0.0010 0.00010 0.0001 0.00001 0.0003

0.0009 0.00009 -0.0008 -0.00008 0.0009 0.00009 0.0003 0.00003 0.0001

-0.0001 -0.00001 0.0005 0.00005 0.0000 0.00000 0.0001 0.00001 0.0001

0.0004 0.00004 0.0011 0.00011 0.0000 0.00000 0.0005 0.00005 0.0003

0.0009 0.00009 0.0013 0.00013 0.0000 0.00000 0.0007 0.00007 0.0006

0.0010 0.00010 0.0011 0.00011 0.0005 0.00005 0.0009 0.00009 0.0007

0.0014 0.00014 0.0013 0.00013 0.0005 0.00005 0.0011 0.00011 0.0007

0.0016 0.00016 0.0013 0.00013 0.0005 0.00005 0.0011 0.00011 0.0009

0.0022 0.00022 0.0016 0.00016 0.0007 0.00007 0.0015 0.00015 0.0012

0.0022 0.00022 0.0016 0.00016 0.0007 0.00007 0.0015 0.00015 0.0013

0.0020 0.00020 0.0016 0.00016 0.0006 0.00006 0.0014 0.00014 0.0011

0.0021 0.00021 0.0016 0.00016 0.0010 0.00010 0.0016 0.00016 0.0013

0.0022 0.00022 0.0016 0.00016 0.0010 0.00010 0.0016 0.00016 0.0014

186

Average total

Strain - 2

Cylinders

Time,m Time, day

(in/in)

(x 10^6)

0 0

0

24 0.0

0.000289984

289.9839

41 0.0

0.000331626

331.6256

83 0.1

0.000376547

376.547

188 0.1

0.000356542

356.5418

384 0.3

0.000346523

346.5229

1227 0.9

0.00044821

448.2097

2534 1.8

0.000488244

488.2435

4090 2.8

0.000514911

514.9113

6898 4.8

0.000559907

559.9069

9853 6.8

0.000603234

603.2337

11488 8.0

0.000643236

643.2363

18720 13.0

0.000696576

696.576

28800 20.0

0.000738241

738.2413

38880 27.0

0.000766575

766.5751

38881 27.0

0.000453265

453.2652

Creep=

Average Shrinkage

Total

Strain - 2

minus

Cylinders

Shrinkage

Time,m Time, day

(in/in)

(x 10^6) (in)

(in/in)

(x 10^6)

0 0

0

0 0.0000

0.000000

0

24 0.0

5.01659E-06

5.016592 0.0029

0.000285

284.9673

41 0.0

2.8308E-05

28.30803 0.0030

0.000303

303.3175

83 0.1

1.32701E-05

13.27013 0.0036

0.000363

363.2769

188 0.1

1.1662E-05

11.66199 0.0035

0.000345

344.8798

384 0.3

3.16538E-05

31.65377 0.0032

0.000315

314.8692

1227 0.9

6.16742E-05

61.67415 0.0039

0.000387

386.5356

2534 1.8

6.66283E-05

66.62833 0.0042

0.000422

421.6152

4090 2.8

6.66125E-05

66.61249 0.0045

0.000448

448.2988

6898 4.8

8.66368E-05

86.63677 0.0047

0.000473

473.2701

9853 6.8

0.000119971

119.9709 0.0048

0.000483

483.2628

11488 8.0

0.000124979

124.9791 0.0052

0.000518

518.2571

18720 13.0

0.000108298

108.2979 0.0059

0.000588

588.2781

28800 20.0

0.000126622

126.622 0.0061

0.000612

611.6194

38880 27.0

0.000134969

134.9687 0.0063

0.000632

631.6064

38881 27.0

0.000134969

134.9687 0.0032

0.000318

318.2965

187

Mix #3

Metakaolin - 5% OPC Replacement

Applied Creep Load =

2140psi Specific

Creep Specific Specific

Time Total Creep Shrinkage plus Initial Creep Total

(min) (in/in) (in/in) (in/in) (microstrain/psi)

(microstrain/psi)

0 0 0 0 0 0

24 .290E-3 .285E-3 .502E-5 0.133 0 0.136

41 .332E-3 .303E-3 .283E-4 0.142 0.009 0.155

83 .377E-3 .363E-3 .133E-4 0.170 0.037 0.176

188 .357E-3 .345E-3 .117E-4 0.161 0.028 0.167

384 .347E-3 .315E-3 .317E-4 0.147 0.014 0.162

1227 .448E-3 .387E-3 .617E-4 0.181 0.047 0.209

2534 .488E-3 .422E-3 .666E-4 0.197 0.064 0.228

4090 .515E-3 .448E-3 .666E-4 0.209 0.076 0.241

6898 .560E-3 .473E-3 .866E-4 0.221 0.088 0.262

9853 .603E-3 .483E-3 .120E-3 0.226 0.093 0.282

11488 .643E-3 .518E-3 .125E-3 0.242 0.109 0.301

18720 .697E-3 .588E-3 .108E-3 0.275 0.142 0.326

28800 .738E-3 .612E-3 .127E-3 0.286 0.153 0.345

.

38881 .453E-3 .318E-3 .135E-3 0.149 0.212

188

Mix Design #4

Metakaolin 10 % OPC Replacement

Mix # 4 - 3rd Alteration - Metakaolin - 10% OPC Replacement* w/c ratio=

0.3338

mix proportions (per)

Concrete Constituent

1 yd

3

1.5 ft

3

Course Aggregate 1770 lb 98.35 lbs

Fine Aggregate 1295 71.95 lbs

Portland Cement Type II 597.5 33.2 lbs

Silica Fume (AASHTO M307)

none none

Fly Ash (AASHTO M295) 100 5.55 lbs-------->

2517.4g

Metakaolin (High Reactive) 77.5 4.3 lbs-------->

1950.4g

Water

255 14.37 lbs

Water Reducer (ASTM C494)

none

Superplasticizer (ASTM C494)

7.0floz/cwt 90 mL

* Based on 775 pounds of total cementitious materials

189

Concrete for Hood Canal Floating Bridge Replacement Project

Concrete Mix Design -

Metakaolin - 10% OPC Replacement

Mix Design # - 4

Date Batched and Specimens Cast - December 14, 2002

Slump - 8.5"

Air Content - -

Batch Temperature - 62 F

Number of specimens cast (6x12 and 4x8) - 7 and 2 (#'s 28-36)

Date drilled and fitted with gage points -

28-day Curing Date - January 11, 2003

28-day Compressive Strength - Break notes

Cylinder f'c-1 =

9340

psi (264,240 lbs) Shear Plane

Cylinder f'c-2 =

9080

psi (256,990 lbs) Two cones

Cylinder f'c-3 =

9200

psi (260,400 lbs) Two cones

Average =

9206.7

psi

Load to Apply for Creep Test - ASTM C 512

= 40% x f'c (28 day)

=.40 x 9207 psi = 3683 psi

Actual Applied Load =

33 tons = 25.4 % f'c (28 day) = 2334.3 psi

Creep and Shrinkage Measurements

31 32

Cylinder C-1 (mix #__4__) Cylinder C-2 (mix #__4__)

Actual date Creep Measurement Creep Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading

2/18 2:20pm 0.1448 0.1567 0.1544 0.1369 0.1502 0.0959

Immediately after Loading

2/18 2:25pm 0.1414 0.153 0.1508 0.1336 0.1471 0.0928

15-20 minutes

2/18 2:40pm 0.1412 0.1532 0.1502 0.133 0.1469 0.0924

1 hour

2/18 3:25pm 0.141 0.1528 0.1501 0.1328 0.1468 0.0922

2 hours: 45 minutes

2/18 5:30pm 0.1411 0.1527 0.1499 0.1324 0.1469 0.0919

6 - 8 hours

2/18 8:50pm 0.141 0.1525 0.1499 0.1323 0.1469 0.092

2nd Day

2/19 5:05p 0.1406 0.152 0.1497 0.1321 0.1463 0.0917

3rd Day

2/20 1:30a 0.1397 0.1514 0.1494 0.1316 0.1454 0.0911

4th Day

2/21 2:05p 0.1395 0.1512 0.1489 0.1314 0.145 0.0909

7th Day

2/24 12:55p 0.1389 0.15 0.148 0.1311 0.1433 0.0888

14th Day

3/3 2:15p 0.1374 0.1488 0.1465 0.1301 0.1425 0.0882

21st Day

3/10 2:25p 0.1366 0.1479 0.1457 0.1292 0.1417 0.0877

28th day

3/17 1:35p 0.1361 0.1481 0.1451 0.1287 0.141 0.087

58th day

5/14 6:00p 0.1338 0.1446 0.1427 0.1269 0.1373 0.0845

recovery

5/14 6:00p 0.1372 0.1487 0.1468 0.1293 0.1426 0.0883

190

Creep and Shrinkage Measurements (Continued)

33 34

Cylinder S-1 (mix #__4__) Cylinder S-2 (mix #__4__)

Actual date Shrinkage Measurement Shrinkage Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading

2/18 2:20pm 0.089 0.1593 0.1517 0.175 0.1552 0.1548

Immediately after Loading

2/18 2:25pm 0.089 0.1592 0.1516 0.1749 0.1551 0.1547

15-20 minutes

2/18 2:40pm 0.0889 0.1592 0.1515 0.1748 0.155 0.1546

1 hour

2/18 3:25pm 0.0888 0.1591 0.1514 0.1747 0.1549 0.1545

2 hours: 45 minutes

2/18 5:30pm 0.0888 0.1591 0.1514 0.1747 0.1549 0.1544

6 - 8 hours

2/18 8:50pm 0.0888 0.159 0.1514 0.1747 0.1549 0.1544

2nd Day

2/19 5:05p 0.0888 0.1589 0.1514 0.1746 0.1549 0.1543

3rd Day

2/20 1:30a 0.0887 0.1588 0.1513 0.1745 0.1548 0.1543

4th Day

2/21 2:05p 0.0887 0.1588 0.1513 0.1745 0.1548 0.1543

7th Day

2/24 12:55p 0.0887 0.1587 0.1513 0.1744 0.1547 0.1543

14th Day

3/3 2:15p 0.0885 0.1584 0.1509 0.1741 0.1545 0.154

21st Day

3/10 2:25p 0.0882 0.1583 0.1507 0.1737 0.1543 0.1538

28th day

3/17 1:35p 0.0881 0.158 0.1505 0.1735 0.1541 0.1535

58th day

5/14 6:00p 0.0865 0.1567 0.1488 0.1721 0.1527 0.152

recovery

5/14 6:00p 0.0865 0.1567 0.1488 0.1721 0.1527 0.152

191

Mix # 4 - Metakaolin -10% OPC Replacement

Creep Measurements



gage zero (10") = 0.1600



Cylinder plane # strain strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

2

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

7

5

8

5

8

r

e

5

8



Shrinkage Measurements

gage zero (10") = 0.1600 average

Cylinder #33 average shrinkage

Cylinder plane shrinkage strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

2

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

7

5

8

5

8

192

r

e

5

8

(creep)

average average Average total

Cylinder #32 total total Strain - 2

Cylinder plane # strain strain Cylinders

1 2 3 (in) (in/in) (in)

0.1369 9.9769 0.1502 9.9902 0.0959 9.9359

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0033 0.00033 0.0031 0.00031 0.0031 0.00031 0.0032 0.00032 0.0034

0.0039 0.00039 0.0033 0.00033 0.0035 0.00035 0.0036 0.00036 0.0037

0.0041 0.00041 0.0034 0.00034 0.0037 0.00037 0.0037 0.00037 0.0039

0.0045 0.00045 0.0033 0.00033 0.0040 0.00040 0.0039 0.00039 0.0040

0.0046 0.00046 0.0033 0.00033 0.0039 0.00039 0.0039 0.00039 0.0041

0.0048 0.00048 0.0039 0.00039 0.0042 0.00042 0.0043 0.00043 0.0044

0.0053 0.00053 0.0048 0.00048 0.0048 0.00048 0.0050 0.00050 0.0051

0.0055 0.00055 0.0052 0.00052 0.0050 0.00050 0.0052 0.00053 0.0053

0.0058 0.00058 0.0069 0.00069 0.0071 0.00071 0.0066 0.00066 0.0065

0.0068 0.00068 0.0077 0.00077 0.0077 0.00077 0.0074 0.00074 0.0076

0.0077 0.00077 0.0085 0.00085 0.0082 0.00083 0.0081 0.00082 0.0084

0.0082 0.00082 0.0092 0.00092 0.0089 0.00090 0.0088 0.00088 0.0088

0.0100 0.00100 0.0129 0.00129 0.0114 0.00115 0.0114 0.00115 0.0115

0.0076 0.00076 0.0076 0.00076 0.0076 0.00076 0.0076 0.00076 0.0077

(shrinkage) average Average Shrinkage

Cylinder #34 average shrinkage Strain - 2

Cylinder plane shrinkage strain Cylinders

1 2 3 strain (in/in) (in)

0.175 10.0150 0.1552 9.9952 0.1548 9.9948

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0001 0.00001 0.0001 0.00001 0.0001 0.00001 0.0001 0.00001 0.0001

0.0002 0.00002 0.0002 0.00002 0.0002 0.00002 0.0002 0.00002 0.0002

0.0003 0.00003 0.0003 0.00003 0.0003 0.00003 0.0003 0.00003 0.0003

0.0003 0.00003 0.0003 0.00003 0.0004 0.00004 0.0003 0.00003 0.0003

0.0004 0.00004 0.0003 0.00003 0.0005 0.00005 0.0004 0.00004 0.0003

0.0005 0.00005 0.0004 0.00004 0.0005 0.00005 0.0005 0.00005 0.0004

0.0006 0.00006 0.0005 0.00005 0.0005 0.00005 0.0005 0.00005 0.0005

0.0009 0.00009 0.0007 0.00007 0.0008 0.00008 0.0008 0.00008 0.0008

0.0013 0.00013 0.0009 0.00009 0.0010 0.00010 0.0011 0.00011 0.0010

0.0015 0.00015 0.0011 0.00011 0.0013 0.00013 0.0013 0.00013 0.0012

0.0029 0.00029 0.0025 0.00025 0.0028 0.00028 0.0027 0.00027 0.0027

193

0.0029 0.00029 0.0025 0.00025 0.0028 0.00028 0.0027 0.00027 0.0027

Average total

Strain - 2

Cylinders

Time,m Time, day

(in/in)

(x 10^-6)

0 0

0

5 0.0

0.000337

337.3183

20 0.0

0.000367

367.3973

65 0.0

0.000387

387.4363

190 0.1

0.000401

400.8156

390 0.3

0.000406

405.8123

1605 1.1

0.000443

442.5436

2830 2.0

0.000506

506.0044

4305 3.0

0.000534

534.3843

8555 5.9

0.000648

648.013

18715 13.0

0.000758

758.1879

28805 20.0

0.000837

836.6555

38835 27.0

0.000883

883.4454

83520 58.0

0.001154

1153.944

83521 58.0

0.000768

768.2092

Creep=

Average Shrinkage

Total

Strain - 2

minus

Cylinders

Shrinkage

Time,m Time, day

(in/in)

(x 10^-6) (in)

(in/in)

(x 10^-6)

0 0

0

0 0.0000

0.000000

0

5 0.0

8.33E-06

8.334006 0.0033

0.000329

328.9842

20 0.0

1.67E-05

16.67981 0.0035

0.000351

350.7175

65 0.0

2.67E-05

26.6924 0.0036

0.000361

360.7439

190 0.1

2.84E-05

28.35994 0.0037

0.000372

372.4557

390 0.3

3E-05

30.02672 0.0038

0.000376

375.7856

1605 1.1

3.5E-05

35.02521 0.0041

0.000408

407.5184

2830 2.0

4.34E-05

43.37026 0.0046

0.000463

462.6341

4305 3.0

4.34E-05

43.37026 0.0049

0.000491

491.014

8555 5.9

4.84E-05

48.36869 0.0060

0.000600

599.6443

18715 13.0

7.67E-05

76.72846 0.0068

0.000681

681.4594

28805 20.0

0.0001

100.0938 0.0074

0.000737

736.5617

38835 27.0

0.000122

121.7747 0.0076

0.000762

761.6707

83520 58.0

0.00027

270.313 0.0088

0.000884

883.6311

194

83521 58.0

0.00027

270.313 0.0050

0.000498

497.8962

Mix #4

Metakaolin - 10% OPC Replacement

Applied Creep Load = 2340psi Specific

Creep Specific Specific

Time Total Creep Shrinkage plus Initial Creep Total

(min) (in/in) (in/in) (in/in) (microstrain/psi)

(microstrain/psi)

0 0 0 0 0 0

5 .337E-3 .329E-3 .833E-5 0.141 0 0.144

20 .367E-3 .351E-3 .167E-4 0.150 0.009 0.157

65 .387E-3 .361E-3 .267E-4 0.154 0.014 0.166

190 .401E-3 .372E-3 .284E-4 0.159 0.019 0.171

390 .406E-3 .376E-3 .300E-4 0.161 0.020 0.173

1605 .443E-3 .408E-3 .350E-4 0.174 0.034 0.189

2830 .506E-3 .463E-3 .434E-4 0.198 0.057 0.216

4305 .534E-3 .491E-3 .434E-4 0.210 0.069 0.228

8555 .648E-3 .600E-3 .484E-4 0.256 0.116 0.277

18715 .758E-3 .681E-3 .767E-4 0.291 0.151 0.324

28805 .837E-3 .737E-3 .100E-3 0.315 0.174 0.358

.

83520 .115E-2 .884E-3 .270E-3 0.378 0.237 0.493

83521 .768E-3 .498E-3 .270E-3 0.213 0.328

195

Mix Design #5

LVM (Phase 2)

Mix # 5 - LVM Mix Design #2

w/c ratio=

0.3342

mix proportions (per)

Concrete Constituent

1 yd

3

1.5 ft

3

Course Aggregate 1770 lb 98.35 lbs

Fine Aggregate 1295 71.95 lbs

Portland Cement Type II 624 34.65 lbs

Silica Fume (AASHTO M307) 50 2.8 lbs

Fly Ash (AASHTO M295) 100 5.55 lbs

Water

258.66 14.37 lbs

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 5.3floz/cwt 65 mL

slurry - Silica fume=2.8 lbs(all)

(1270.05grams) Mix Water=total-slurry water

Water=3.42lbs (1551.28grams) =

10.73

lbs

HRWR=6mL

196

Concrete for Hood Canal Floating Bridge Replacement Project

Concrete Mix Design -

LVM Mix Design (2nd), Reference Mix

Mix Design # - 5

Date Batched and Specimens Cast - December 14, 2002

Slump - 8.5"

Air Content - -

Batch Temperature - 62 F

Number of specimens cast (6x12 and 4x8) - 7 and 2 (#'s 37-45)

Date drilled and fitted with gage points -

28-day Curing Date - January 11, 2003

28-day Compressive Strength - Break notes

Cylinder f'c-1 =

8870

psi (251,000 lbs) 2 cones

Cylinder f'c-2 =

8820

psi (249,550 lbs) Cone/Shear

Cylinder f'c-3 =

8910

psi (252,040 lbs) Cone/Shear

Average =

8866.7

psi

Load to Apply for Creep Test - ASTM C 512

= 40% x f'c (28 day)

=.40 x 8867 psi = 3547 psi

Actual Applied Load =

30.6 tons = 24.4 % f'c (28 day) = 2163.6 psi

Creep and Shrinkage Measurements

40 41

Cylinder C-1 (mix #__5__) Cylinder C-2 (mix #__5__)

Actual date Creep Measurement Creep Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading

2/18 2:30pm 0.154 0.1566 0.1519 0.1538 0.1548 0.1571

Immediately after Loading

2/18 2:35pm 0.1506 0.153 0.149 0.1509 0.1509 0.153

15-20 minutes

2/18 2:58pm 0.1502 0.1527 0.1478 0.1505 0.1508 0.1532

1 hour

2/18 3:35pm 0.15 0.1526 0.1477 0.1504 0.1507 0.1527

2 hours: 45 minutes

2/18 5:35pm 0.1499 0.1524 0.1476 0.1501 0.1505 0.1525

6 - 8 hours

2/18 8:55pm 0.1499 0.1522 0.1474 0.1498 0.1504 0.1523

2nd Day

2/19 5:10p 0.1496 0.1519 0.1474 0.1496 0.15 0.1521

3rd Day

2/20 1:40a 0.149 0.1516 0.1469 0.1489 0.1493 0.1515

4th Day

2/21 2:07p 0.149 0.1514 0.1469 0.1487 0.1493 0.1512

7th Day

2/24 1:00p 0.1483 0.1505 0.1461 0.1481 0.1484 0.1502

14th Day

3/3 2:25p 0.1474 0.1497 0.1452 0.1472 0.1476 0.1491

21st Day

3/10 2:30p 0.1466 0.1488 0.1445 0.1463 0.147 0.1483

28th day

3/17 1:40p 0.1463 0.1484 0.1439 0.146 0.1462 0.148

58th day

5/14 6:00p 0.1446 0.1462 0.1422 0.1445 0.1442 0.1461

recovery

5/14 6:00p 0.1483 0.1501 0.146 0.1482 0.1488 0.1507

197

Creep and Shrinkage Measurements (Continued)

42 43

Cylinder S-1 (mix #__5__) Cylinder S-2 (mix #__5__)

Actual date Shrinkage Measurement Shrinkage Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading2/18 2:30pm 0.1422 0.1585 0.1421 0.1529 0.1605 0.1536

Immediately after Loading2/18 2:35pm 0.1421 0.1585 0.1421 0.1529 0.1605 0.1536

15-20 minutes2/18 2:58pm 0.1421 0.1583 0.142 0.1528 0.1604 0.1535

1 hour2/18 3:35pm 0.142 0.1582 0.1419 0.1527 0.1603 0.1535

2 hours: 45 minutes2/18 5:35pm 0.1421 0.1581 0.1419 0.1527 0.1603 0.1535

6 - 8 hours2/18 8:55pm 0.1421 0.1581 0.1419 0.1526 0.1602 0.1535

2nd Day2/19 5:10p 0.1421 0.1581 0.1418 0.1525 0.1602 0.1534

3rd Day2/20 1:40a 0.1421 0.1581 0.1418 0.1525 0.1602 0.1533

4th Day2/21 2:07p 0.142 0.1581 0.1417 0.1524 0.1601 0.1533

7th Day2/24 1:00p 0.1419 0.1581 0.1417 0.1524 0.1601 0.1533

14th Day3/3 2:25p 0.1419 0.1579 0.1414 0.1522 0.16 0.1532

21st Day3/10 2:30p 0.1417 0.1579 0.1413 0.1522 0.1598 0.1531

28th day3/17 1:40p 0.1416 0.1576 0.1412 0.152 0.1594 0.153

58th day5/14 6:00p 0.1411 0.1564 0.1401 0.1503 0.1585 0.1517

recovery5/14 6:00p 0.1411 0.1564 0.1401 0.1503 0.1585 0.1517

198



Mix # 5 -2nd LVM Mix Design

gage zero (10") = 0.1600



(

c



Cylinder #40 total total

Cylinder plane # strain strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

2

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

7

5

8

5

8

r

e

5

8



Shrinkage Measurements

gage zero (10") = 0.1600 average

Cylinder #42 average shrinkage

Cylinder plane shrinkage strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

2

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

7

5

8

5

8

r

e

5

8

199

(creep)

average average Average total

Cylinder #41 total total Strain - 2

Cylinder plane # strain strain Cylinders

1 2 3 (in) (in/in) (in)

0.1538 9.9938 0.1548 9.9948 0.1571 9.9971

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0029 0.00029 0.0039 0.00039 0.0041 0.00041 0.0036 0.00036 0.0035

0.0033 0.00033 0.0040 0.00040 0.0039 0.00039 0.0037 0.00037 0.0038

0.0034 0.00034 0.0041 0.00041 0.0044 0.00044 0.0040 0.00040 0.0040

0.0037 0.00037 0.0043 0.00043 0.0046 0.00046 0.0042 0.00042 0.0042

0.0040 0.00040 0.0044 0.00044 0.0048 0.00048 0.0044 0.00044 0.0044

0.0042 0.00042 0.0048 0.00048 0.0050 0.00050 0.0047 0.00047 0.0046

0.0049 0.00049 0.0055 0.00055 0.0056 0.00056 0.0053 0.00053 0.0052

0.0051 0.00051 0.0055 0.00055 0.0059 0.00059 0.0055 0.00055 0.0053

0.0057 0.00057 0.0064 0.00064 0.0069 0.00069 0.0063 0.00063 0.0061

0.0066 0.00066 0.0072 0.00072 0.0080 0.00080 0.0073 0.00073 0.0070

0.0075 0.00075 0.0078 0.00078 0.0088 0.00088 0.0080 0.00080 0.0078

0.0078 0.00078 0.0086 0.00086 0.0091 0.00091 0.0085 0.00085 0.0082

0.0093 0.00093 0.0106 0.00106 0.0110 0.00110 0.0103 0.00103 0.0101

0.0056 0.00056 0.0060 0.00060 0.0064 0.00064 0.0060 0.00060 0.0060

(shrinkage) average Average Shrinkage

Cylinder #43 average shrinkage Strain - 2

Cylinder plane shrinkage strain Cylinders

1 2 3 strain (in/in) (in)

0.1529 9.9929 0.1605 10.0005 0.1536 9.9936

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0001 0.00001 0.0001 0.00001 0.0001 0.00001 0.0001 0.00001 0.0001

0.0002 0.00002 0.0002 0.00002 0.0001 0.00001 0.0002 0.00002 0.0002

0.0003 0.00003 0.0003 0.00003 0.0001 0.00001 0.0002 0.00002 0.0002

0.0004 0.00004 0.0003 0.00003 0.0002 0.00002 0.0003 0.00003 0.0003

0.0004 0.00004 0.0003 0.00003 0.0003 0.00003 0.0003 0.00003 0.0003

0.0005 0.00005 0.0004 0.00004 0.0003 0.00003 0.0004 0.00004 0.0004

0.0007 0.00007 0.0005 0.00005 0.0004 0.00004 0.0005 0.00005 0.0005

0.0007 0.00007 0.0007 0.00007 0.0005 0.00005 0.0006 0.00006 0.0006

0.0009 0.00009 0.0011 0.00011 0.0006 0.00006 0.0009 0.00009 0.0008

0.0026 0.00026 0.0020 0.00020 0.0019 0.00019 0.0022 0.00022 0.0020

200

Average total

Strain - 2

Cylinders

(microstrain)

Time,m Time, day

(in/in)

(x 10^6)

0 0

0

5 0.0

0.000347

346.84

28 0.0

0.000384

383.54

65 0.0

0.000402

401.88

185 0.1

0.000420

420.22

385 0.3

0.000437

436.90

1600 1.1

0.000460

460.24

2830 2.0

0.000517

516.94

4297 3.0

0.000529

528.61

8550 5.9

0.000610

610.32

18710 13.0

0.000700

700.37

28800 20.0

0.000779

778.74

38830 27.0

0.000824

823.76

83520 58.0

0.001007

1007.19

83521 58.0

0.000602

601.98

Creep=

Average Shrinkage

Total

Strain - 2

minus

Cylinders

(microstrain) Shrinkage

Shrinkage

(microstrain)

Time,m Time, day

(in/in)

(x 10^6) (in)

(in/in)

(x 10^6)

0 0

0

0 0.0000

0.000000

0

5 0.0

1.668E-06

1.668 0.0034

0.000345

345.18

28 0.0

1.167E-05

11.673 0.0037

0.000372

371.86

65 0.0

2.001E-05

20.011 0.0038

0.000382

381.87

185 0.1

2.001E-05

20.010 0.0040

0.000400

400.21

385 0.3

2.335E-05

23.345 0.0041

0.000414

413.55

1600 1.1

2.835E-05

28.348 0.0043

0.000432

431.89

2830 2.0

3.002E-05

30.016 0.0049

0.000487

486.92

4297 3.0

3.669E-05

36.686 0.0049

0.000492

491.92

8550 5.9

3.835E-05

38.354 0.0057

0.000572

571.96

18710 13.0

5.336E-05

53.363 0.0065

0.000647

647.00

28800 20.0

6.337E-05

63.368 0.0072

0.000715

715.37

38830 27.0

8.338E-05

83.378 0.0074

0.000740

740.39

83520 58.0

1.951E-04

195.103 0.0081

0.000812

812.09

83521 58.0

1.951E-04

195.103 0.0041

0.000407

406.88

201

Mix #5

LVM Mix Design, Reference Mix (Phase 2)

Applied Creep Load =

2160psi Specific

Creep Specific Specific

Time Total Creep Shrinkage plus Initial Creep Total

(min) (in/in) (in/in) (in/in) (microstrain/psi)

(microstrain/psi)

0 0 0 0 0 0

5 .347E-3 .345E-3 .167E-5 0.160 0 0.161

28 .384E-3 .372E-3 .117E-4 0.172 0.012 0.178

65 .402E-3 .382E-3 .200E-4 0.177 0.017 0.186

185 .420E-3 .400E-3 .200E-4 0.185 0.025 0.195

385 .437E-3 .414E-3 .233E-4 0.191 0.032 0.202

1600 .460E-3 .432E-3 .283E-4 0.200 0.040 0.213

2830 .517E-3 .487E-3 .300E-4 0.225 0.066 0.239

4297 .529E-3 .492E-3 .367E-4 0.228 0.068 0.245

8550 .610E-3 .572E-3 .384E-4 0.265 0.105 0.283

18710 .700E-3 .647E-3 .534E-4 0.300 0.140 0.324

28800 .779E-3 .715E-3 .634E-4 0.331 0.171 0.361

.

83520 .101E-2 .812E-3 .195E-3 0.376 0.216 0.466

83521 .602E-3 .407E-3 .195E-3 0.188 0.279

202

Mix Design #6

LVM Mix with Caltite Waterproofing Admixture

Mix # 6 - 4th Alteration - LVM Mix with Caltite Admixture w/c ratio=

0.3514

mix proportions (per)

Concrete Constituent

1 yd

3

1.5 ft

3

Course Aggregate 1770 lb 98.35 lbs

Fine Aggregate 1295 71.95 lbs

Portland Cement Type II 624 34.65 lbs

Silica Fume (AASHTO M307) 50 2.8 lbs

Fly Ash (AASHTO M295) 100 5.55 lbs

Water

222.12 12.34 lbs

Water Reducer (ASTM C494) none

Superplasticizer (ASTM C494) 5.5floz/cwt 70 mL

Caltite 6 gallons 2.77 lbs



Slurry - Silica fume=2.8 lbs(all)

(1270.05grams) Mix Water=total-slurry water

Water=3.42lbs (1551.28grams) =

8.92

lbs

HRWR=6mL

203

Concrete for Hood Canal Floating Bridge Replacement Project

Concrete Mix Design -

LVM Mix with Caltite Waterproofing Admixture

Mix Design # - 6

Date Batched and Specimens Cast - December 14, 2002

Slump - 8.5"

Air Content - -

Batch Temperature - 62 F

Number of specimens cast (6x12 and 4x8) - 7 and 2 (#'s 46-54)

Date drilled and fitted with gage points -

28-day Curing Date - January 11, 2003

28-day Compressive Strength - Break notes

Cylinder f'c-1 =

7010psi (198,330 lbs) Cone/Shear

Cylinder f'c-2 =

6800psi (192,420 lbs) Shear Plane

Cylinder f'c-3 =

6860psi (194,190 lbs) Cone/Shear

Average =

6890psi

Load to Apply for Creep Test - ASTM C 512

= 40% x f'c (28 day)

=.40 x 6890 psi = 2756 psi

Actual Applied Load =

23.8 tons = 24.4 % f'c (28 day) = 1681.2 psi

Creep and Shrinkage Measurements

49 50

Cylinder C-1 (mix #__6__) Cylinder C-2 (mix #__6__)

Actual date Creep Measurement Creep Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading

2/18 2:45pm 0.1114 0.1594 0.1509 0.1614 0.1592 0.1771

Immediately after Loading

2/18 2:55pm 0.1084 0.1568 0.1475 0.1588 0.1572 0.173

15-20 minutes

2/18 3:10pm 0.1083 0.1568 0.1473 0.1586 0.1574 0.1728

1 hour

2/18 3:55pm 0.1081 0.1564 0.147 0.1585 0.157 0.1725

2 hours: 45 minutes

2/18 5:40pm 0.1078 0.1562 0.1466 0.1581 0.1569 0.1722

6 - 8 hours

2/18 9:00pm 0.1077 0.1558 0.1465 0.158 0.1568 0.172

2nd Day

2/19 5:15p 0.1075 0.1558 0.146 0.1577 0.1565 0.1718

3rd Day

2/20 1:45a 0.107 0.1554 0.1454 0.1572 0.1562 0.1712

4th Day

2/21 2:10p 0.107 0.1554 0.145 0.1574 0.1563 0.1708

7th Day

2/24 1:05p 0.1064 0.1547 0.1444 0.1569 0.1558 0.1702

14th Day

3/3 2:30p 0.1054 0.1542 0.1434 0.1561 0.1548 0.169

21st Day

3/10 2:35p 0.1048 0.1533 0.1424 0.1553 0.1542 0.1682

28th day

3/17 1:45p 0.1044 0.1529 0.1421 0.1549 0.1538 0.1678

58th day

5/14 6:00p 0.1026 0.1513 0.1402 0.1531 0.1523 0.1659

recovery

5/14 6:00p 0.1057 0.1541 0.144 0.1564 0.1548 0.1703

204

Creep and Shrinkage Measurements (Continued)

51 52

Cylinder S-1 (mix #__6__) Cylinder S-2 (mix #__6__)

Actual date Shrinkage Measurement Shrinkage Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading2/18 2:45pm 0.154 0.1551 0.152 0.162 0.1631 0.156

Immediately after Loading2/18 2:55pm 0.154 0.1551 0.152 0.162 0.1631 0.156

15-20 minutes2/18 3:10pm 0.1539 0.155 0.1518 0.1619 0.1629 0.1559

1 hour2/18 3:55pm 0.1538 0.155 0.1517 0.1618 0.1628 0.1558

2 hours: 45 minutes2/18 5:40pm 0.1538 0.155 0.1517 0.1618 0.1627 0.1558

6 - 8 hours2/18 9:00pm 0.1538 0.1549 0.1516 0.1618 0.1627 0.1557

2nd Day2/19 5:15p 0.1537 0.1548 0.1513 0.1617 0.1626 0.1556

3rd Day2/20 1:45a 0.1536 0.1547 0.1511 0.1616 0.1625 0.1554

4th Day2/21 2:10p 0.1536 0.1547 0.1511 0.1616 0.1625 0.1554

7th Day2/24 1:05p 0.1536 0.1547 0.151 0.1616 0.1625 0.1553

14th Day3/3 2:30p 0.1533 0.1545 0.1507 0.1615 0.1623 0.1551

21st Day3/10 2:35p 0.1531 0.1542 0.1506 0.1613 0.1622 0.1548

28th day3/17 1:45p 0.1528 0.1541 0.1504 0.1613 0.1621 0.1545

58th day5/14 6:00p 0.1519 0.153 0.1492 0.1601 0.1614 0.1531

recovery5/14 6:00p 0.1519 0.153 0.1492 0.1601 0.1614 0.1531

205

Mix #6 - LVM Mix w/ Caltite

gage zero (10") = 0.1600



(

c



Cylinder #49 total total

Cylinder plane # strain strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

2

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

7

5

8

5

8

r

e

5

8



Shrinkage Measurements

gage zero (10") =

0.1600

average

Cylinder #51 average shrinkage

Cylinder plane shrinkage strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

2

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

7

5

8

5

8

r

e

5

8

206

(creep)

average average Average total

Cylinder #50 total total Strain - 2

Cylinder plane # strain strain Cylinders

1 2 3

(in) (in/in) (in)

0.1614 10.0014 0.1592 9.9992 0.1771 10.0171

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0026 0.00026 0.0020 0.00020 0.0041 0.00041 0.0029 0.00029 0.0030

0.0028 0.00028 0.0018 0.00018 0.0043 0.00043 0.0030 0.00030 0.0030

0.0029 0.00029 0.0022 0.00022 0.0046 0.00046 0.0032 0.00032 0.0033

0.0033 0.00033 0.0023 0.00023 0.0049 0.00049 0.0035 0.00035 0.0036

0.0034 0.00034 0.0024 0.00024 0.0051 0.00051 0.0036 0.00036 0.0038

0.0037 0.00037 0.0027 0.00027 0.0053 0.00053 0.0039 0.00039 0.0040

0.0042 0.00042 0.0030 0.00030 0.0059 0.00059 0.0044 0.00044 0.0045

0.0040 0.00040 0.0029 0.00029 0.0063 0.00063 0.0044 0.00044 0.0046

0.0045 0.00045 0.0034 0.00034 0.0069 0.00069 0.0049 0.00049 0.0052

0.0053 0.00053 0.0044 0.00044 0.0081 0.00081 0.0059 0.00059 0.0061

0.0061 0.00061 0.0050 0.00050 0.0089 0.00089 0.0067 0.00067 0.0069

0.0065 0.00065 0.0054 0.00054 0.0093 0.00093 0.0071 0.00071 0.0072

0.0083 0.00083 0.0069 0.00069 0.0112 0.00112 0.0088 0.00088 0.0090

0.0050 0.00050 0.0044 0.00044 0.0068 0.00068 0.0054 0.00054 0.0057

(shrinkage) average Average Shrinkage

Cylinder #52 average shrinkage Strain - 2

Cylinder plane shrinkage strain Cylinders

1 2 3

strain (in/in) (in)

0.162 10.0020 0.1631 10.0031 0.156 9.9960

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0001 0.00001 0.0002 0.00002 0.0001 0.00001 0.0001 0.00001 0.0001

0.0002 0.00002 0.0003 0.00003 0.0002 0.00002 0.0002 0.00002 0.0002

0.0002 0.00002 0.0004 0.00004 0.0002 0.00002 0.0003 0.00003 0.0002

0.0002 0.00002 0.0004 0.00004 0.0003 0.00003 0.0003 0.00003 0.0003

0.0003 0.00003 0.0005 0.00005 0.0004 0.00004 0.0004 0.00004 0.0004

0.0004 0.00004 0.0006 0.00006 0.0006 0.00006 0.0005 0.00005 0.0005

0.0004 0.00004 0.0006 0.00006 0.0007 0.00007 0.0006 0.00006 0.0006

0.0005 0.00005 0.0008 0.00008 0.0009 0.00009 0.0007 0.00007 0.0008

0.0007 0.00007 0.0009 0.00009 0.0012 0.00012 0.0009 0.00009 0.0010

0.0007 0.00007 0.0010 0.00010 0.0015 0.00015 0.0011 0.00011 0.0012

0.0019 0.00019 0.0017 0.00017 0.0029 0.00029 0.0022 0.00022 0.0023

207

Average total

Strain - 2

Cylinders

Time,m Time, day

(in/in)

(x 10^-6)

0 0

0

5 0.0

0.000295

295.1784

20 0.0

0.000304

303.5164

65 0.0

0.000332

331.8628

170 0.1

0.000360

360.2175

370 0.3

0.000377

376.8884

1585 1.1

0.000402

401.9063

2815 2.0

0.000450

450.272

4280 3.0

0.000459

458.6003

8535 5.9

0.000517

516.9747

18700 13.0

0.000609

608.7038

28785 20.0

0.000687

687.0782

38815 27.0

0.000725

725.4373

83520 58.0

0.000901

900.558

83521 58.0

0.000569

568.7081

Creep=

Average Shrinkage

Total

Strain - 2

minus

Cylinders

Shrinkage

Time,m Time, day

(in/in)

(x 10^-6) (in)

(in/in)

(x 10^-6)

0 0

0

0 0.0000

0.000000

0

5 0.0

0

0 0.0030

0.000295

295.1784

20 0.0

1.3E-05

13.3418 0.0029

0.000290

290.1746

65 0.0

2.2E-05

21.68184 0.0031

0.000310

310.1809

170 0.1

2.3E-05

23.34864 0.0034

0.000337

336.8688

370 0.3

2.8E-05

28.34742 0.0035

0.000349

348.541

1585 1.1

4.2E-05

41.6906 0.0036

0.000360

360.2157

2815 2.0

5.5E-05

55.02942 0.0040

0.000395

395.2426

4280 3.0

5.5E-05

55.02942 0.0040

0.000404

403.5709

8535 5.9

5.8E-05

58.36142 0.0046

0.000459

458.6133

18700 13.0

8.0E-05

80.05161 0.0053

0.000529

528.6522

28785 20.0

1.0E-04

100.0608 0.0059

0.000587

587.0174

38815 27.0

1.2E-04

116.7467 0.0061

0.000609

608.6906

83520 58.0

2.3E-04

225.1309 0.0068

0.000675

675.4271

83521 58.0

2.3E-04

225.1309 0.0034

0.000344

343.5772

208

Mix #6

LVM Mix with Caltite Waterproofing Admixture

Applied Creep Load = 1680 psi Specific

Creep Specific Specific

Time Total Creep Shrinkage plus Initial Creep Total

(min) (in/in) (in/in) (in/in) (microstrain/psi)

(microstrain/psi)

0 0 0 0 0 0

5 .295E-3 .295E-3 .000E+0 0.176 0 0.176

20 .304E-3 .290E-3 .133E-4 0.173 -0.003 0.181

65 .332E-3 .310E-3 .217E-4 0.185 0.009 0.198

170 .360E-3 .337E-3 .233E-4 0.201 0.025 0.214

370 .377E-3 .349E-3 .283E-4 0.207 0.032 0.224

1585 .402E-3 .360E-3 .417E-4 0.214 0.039 0.239

2815 .450E-3 .395E-3 .550E-4 0.235 0.060 0.268

4280 .459E-3 .404E-3 .550E-4 0.240 0.065 0.273

8535 .517E-3 .459E-3 .584E-4 0.273 0.097 0.308

18700 .609E-3 .529E-3 .801E-4 0.315 0.139 0.362

28785 .687E-3 .587E-3 .100E-3 0.349 0.174 0.409

.

83520 .901E-3 .675E-3 .225E-3 0.402 0.226 0.536

83521 .569E-3 .344E-3 .225E-3 0.205 0.339

209

Mix Design #7

Caltite Mix Design

Mix # 7 - 5th Alteration - Mix w/Caltite w/o Silica Fume

w/c ratio=

0.2826

mix proportions (per)

Concrete Constituent

1 yd

3

1.5 ft

3

Course Aggregate 1770 lb 98.35 lbs

Fine Aggregate 1295 71.95 lbs

Portland Cement Type II 624 34.65 lbs

Silica Fume (AASHTO M307)

none none lbs

Fly Ash (AASHTO M295) 100 5.55 lbs

Water

154.64 8.59 lbs

Water Reducer (ASTM C494)

none

Superplasticizer (ASTM C494)

6.3floz/cwt 75 mL

Caltite 6 gallons 2.77 lbs

210

Concrete for Hood Canal Floating Bridge Replacement Project

Concrete Mix Design -

Caltite Mix Design

Mix Design # - 7

Date Batched and Specimens Cast - December 14, 2002

Slump - 9.0"

Air Content - -

Batch Temperature - 62 F

Number of specimens cast (6x12 and 4x8) - 7 and 2 (#'s 55-63)

Date drilled and fitted with gage points -

28-day Curing Date - January 11, 2003

28-day Compressive Strength - Break notes

Cylinder f'c-1 = 6100psi (172,550 lbs) Vertical Planes

Cylinder f'c-2 = 6350psi (179,770 lbs) Crushing

Cylinder f'c-3 = 6250psi (176,790 lbs) Crushing

Average = 6233.3psi

Load to Apply for Creep Test - ASTM C 512

= 40% x f'c (28 day)

=.40 x 6233.3 psi = 2493 psi

Actual Applied Load =

21.5 tons = 24.4 % f'c (28 day) = 1520.9 psi

Creep and Shrinkage Measurements

58 59

Cylinder C-1 (mix #__7__) Cylinder C-2 (mix #__7__)

Actual date Creep Measurement Creep Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading2/18 3:05pm 0.152 0.1585 0.1505 0.1354 0.1419 0.1165

Immediately after Loading2/18 3:10pm 0.1507 0.1562 0.1484 0.134 0.1379 0.1143

15-20 minutes2/18 3:25pm 0.1505 0.1561 0.148 0.134 0.1377 0.1141

1 hour2/18 4:25pm 0.1504 0.1558 0.148 0.1338 0.1377 0.1141

2 hours: 45 minutes2/18 5:45pm 0.1502 0.1554 0.1478 0.1332 0.1372 0.1139

6 - 8 hours2/18 9:05pm 0.1499 0.1553 0.1476 0.1328 0.137 0.1138

2nd Day2/19 5:20p 0.1497 0.155 0.1475 0.1326 0.1368 0.1137

3rd Day2/20 1:50a 0.1494 0.1545 0.1472 0.1323 0.1366 0.1132

4th Day2/21 2:15p 0.1496 0.1543 0.1475 0.1324 0.1363 0.1133

7th Day2/24 1:10p 0.1489 0.1535 0.1472 0.1314 0.1355 0.1127

14th Day3/3 2:35p 0.1486 0.1527 0.1467 0.1308 0.1346 0.1122

21st Day3/10 2:40p 0.1481 0.1521 0.1461 0.1302 0.1336 0.1116

28th day3/17 1:50p 0.1478 0.1517 0.1457 0.13 0.1327 0.1109

58th day5/14 6:00p 0.1462 0.149 0.1435 0.1284 0.1303 0.1092

recovery5/14 6:00p 0.1483 0.1521 0.1458 0.1298 0.1344 0.1115

211

Creep and Shrinkage Measurements (Continued)

60 61

Cylinder S-1 (mix #__7__) Cylinder S-2 (mix #__7__)

Actual date Shrinkage Measurement Shrinkage Measurement

Scheduled Time

and time 1 2 3 1 2 3

Before Loading2/18 2:45pm 0.1557 0.1582 0.1575 0.1581 0.1558 0.1532

Immediately after Loading2/18 2:55pm 0.1557 0.1582 0.1575 0.1581 0.1558 0.1532

15-20 minutes2/18 3:10pm 0.1556 0.1582 0.1574 0.1579 0.1557 0.1531

1 hour2/18 3:55pm 0.1555 0.1581 0.1573 0.1578 0.1556 0.153

2 hours: 45 minutes2/18 5:40pm 0.1555 0.1581 0.1573 0.1577 0.1556 0.153

6 - 8 hours2/18 9:00pm 0.1554 0.1581 0.1573 0.1576 0.1556 0.153

2nd Day2/19 5:15p 0.1553 0.158 0.1572 0.1575 0.1555 0.1528

3rd Day2/20 1:45a 0.1552 0.1579 0.1571 0.1575 0.1555 0.1527

4th Day2/21 2:10p 0.1552 0.1578 0.157 0.1575 0.1556 0.1527

7th Day2/24 1:05p 0.1551 0.1577 0.1569 0.1575 0.1556 0.1527

14th Day3/3 2:30p 0.155 0.1575 0.1567 0.1573 0.1554 0.1526

21st Day3/10 2:35p 0.1548 0.1572 0.1565 0.1569 0.1552 0.1522

28th day3/17 1:45p 0.1546 0.1569 0.1563 0.1564 0.1547 0.1519

58th day5/14 6:00p 0.1533 0.1556 0.1553 0.1554 0.1537 0.1512

recovery5/14 6:00p 0.1533 0.1556 0.1553 0.1554 0.1537 0.1512

212

Mix #7 - Caltite Mix Design

gage zero (10") = 0.1600



(

c



Cylinder #58 total total

Cylinder plane # strain strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

1

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

6

5

8

5

8

r

e

5

8



Shrinkage Measurements

gage zero (10") =

0.1600

average

Cylinder #60 average shrinkage

Cylinder plane shrinkage strain

T

i



0



0

.

0

.

0

.

0

.

0

.

1

.

1

.

3

.

5

.

1

4

1

3

2

1

2

0

2

8

2

6

5

8

5

8

r

e

5

8

213

(creep)

average average Average total

Cylinder #59 total total Strain - 2

Cylinder plane # strain strain Cylinders

1 2

3

(in) (in/in) (in)

0.1354 9.9754 0.1419 9.9819 0.1165 9.9565

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0014 0.00014 0.0040 0.00040 0.0022 0.00022 0.0025 0.00025 0.0022

0.0014 0.00014 0.0042 0.00042 0.0024 0.00024 0.0027 0.00027 0.0024

0.0016 0.00016 0.0042 0.00042 0.0024 0.00024 0.0027 0.00027 0.0025

0.0022 0.00022 0.0047 0.00047 0.0026 0.00026 0.0032 0.00032 0.0029

0.0026 0.00026 0.0049 0.00049 0.0027 0.00027 0.0034 0.00034 0.0031

0.0028 0.00028 0.0051 0.00051 0.0028 0.00028 0.0036 0.00036 0.0033

0.0031 0.00031 0.0053 0.00053 0.0033 0.00033 0.0039 0.00039 0.0036

0.0030 0.00030 0.0056 0.00056 0.0032 0.00032 0.0039 0.00039 0.0036

0.0040 0.00040 0.0064 0.00064 0.0038 0.00038 0.0047 0.00047 0.0043

0.0046 0.00046 0.0073 0.00073 0.0043 0.00043 0.0054 0.00054 0.0049

0.0052 0.00052 0.0083 0.00083 0.0049 0.00049 0.0061 0.00061 0.0055

0.0054 0.00054 0.0092 0.00092 0.0056 0.00056 0.0067 0.00068 0.0060

0.0070 0.00070 0.0116 0.00116 0.0073 0.00073 0.0086 0.00087 0.0080

0.0056 0.00056 0.0075 0.00075 0.0050 0.00050 0.0060 0.00060 0.0055

(shrinkage) average Average Shrinkage

Cylinder #61 average shrinkage Strain - 2

Cylinder plane shrinkage strain Cylinders

1 2

3

strain (in/in) (in)

0.1581 9.9981 0.1558 9.9958 0.1532 9.9932

0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000 0.00000 0.0000

0.0002 0.00002 0.0001 0.00001 0.0001 0.00001 0.0001 0.00001 0.0001

0.0003 0.00003 0.0002 0.00002 0.0002 0.00002 0.0002 0.00002 0.0002

0.0004 0.00004 0.0002 0.00002 0.0002 0.00002 0.0003 0.00003 0.0002

0.0005 0.00005 0.0002 0.00002 0.0002 0.00002 0.0003 0.00003 0.0003

0.0006 0.00006 0.0003 0.00003 0.0004 0.00004 0.0004 0.00004 0.0004

0.0006 0.00006 0.0003 0.00003 0.0005 0.00005 0.0005 0.00005 0.0004

0.0006 0.00006 0.0002 0.00002 0.0005 0.00005 0.0004 0.00004 0.0005

0.0008 0.00008 0.0004 0.00004 0.0006 0.00006 0.0006 0.00006 0.0007

0.0012 0.00012 0.0006 0.00006 0.0010 0.00010 0.0009 0.00009 0.0009

0.0017 0.00017 0.0011 0.00011 0.0013 0.00013 0.0014 0.00014 0.0013

0.0027 0.00027 0.0021 0.00021 0.0020 0.00020 0.0023 0.00023 0.0023

214

Average total

Strain - 2

Cylinders

(microstrain)

Time,m Time, day

(in/in)

(x 10^-6)

0 0

0

5 0.0

0.000222

222.1

20 0.0

0.000240

240.4

80 0.1

0.000250

250.4

160 0.1

0.000285

285.5

360 0.3

0.000307

307.2

1571 1.1

0.000326

325.6

2805 1.9

0.000361

360.6

4267 3.0

0.000357

357.3

8525 5.9

0.000427

427.4

18690 13.0

0.000488

487.5

28775 20.0

0.000553

552.6

38805 26.9

0.000601

601.1

83520 58.0

0.000805

804.7

83521 58.0

0.000549

549.3

Creep=

Average Shrinkage

Total

Strain - 2

minus

Cylinders

(microstrain) Shrinkage

Shrinkage

(microstrain)

Time,m Time, day

(in/in)

(x 10^-6) (in)

(in/in)

(x 10^-6)

0 0

0

0 0.0000

0.000000

0

5 0.0

0

0 0.0022

0.000222

222.1

20 0.0

1.00E-05

10.0 0.0023

0.000230

230.4

80 0.1

2.00E-05

20.0 0.0023

0.000230

230.4

160 0.1

2.17E-05

21.7 0.0026

0.000264

263.8

360 0.3

2.50E-05

25.0 0.0028

0.000282

282.2

1571 1.1

3.67E-05

36.7 0.0029

0.000289

288.8

2805 1.9

4.34E-05

43.4 0.0032

0.000317

317.2

4267 3.0

4.51E-05

45.1 0.0031

0.000312

312.2

8525 5.9

5.01E-05

50.1 0.0038

0.000377

377.3

18690 13.0

6.68E-05

66.8 0.0042

0.000421

420.7

28775 20.0

9.52E-05

95.2 0.0046

0.000457

457.5

38805 26.9

1.29E-04

128.6 0.0047

0.000472

472.5

83520 58.0

2.34E-04

233.7 0.0057

0.000571

571.0

83521 58.0

2.34E-04

233.7 0.0032

0.000316

315.6

215

Mix #7

Caltite Mix Design

Applied Creep Load = 1520psi Specific

Creep Specific Specific

Time Total Creep Shrinkage plus Initial Creep Total

(min) (in/in) (in/in) (in/in) (microstrain/psi)

(microstrain/psi)

0 0 0 0 0 0

5 .222E-3 .222E-3 .000E+0 0.146 0 0.146

20 .240E-3 .230E-3 .100E-4 0.152 0.005 0.158

80 .250E-3 .230E-3 .200E-4 0.152 0.005 0.165

160 .285E-3 .264E-3 .217E-4 0.174 0.027 0.188

360 .307E-3 .282E-3 .250E-4 0.186 0.040 0.202

1571 .326E-3 .289E-3 .367E-4 0.190 0.044 0.214

2805 .361E-3 .317E-3 .434E-4 0.209 0.063 0.237

4267 .357E-3 .312E-3 .451E-4 0.205 0.059 0.235

8525 .427E-3 .377E-3 .501E-4 0.248 0.102 0.281

18690 .488E-3 .421E-3 .668E-4 0.277 0.131 0.321

28775 .553E-3 .457E-3 .952E-4 0.301 0.155 0.364

.

83520 .805E-3 .571E-3 .234E-3 0.376 0.230 0.529

83521 .549E-3 .316E-3 .234E-3 0.208 0.361

216

APPENDIX B

EXPERIMENT 2

B1. - Water level changes – second experiment – stage one.

Water Column Height

Specimen

A1 B1 C1 D1

Time

Air Pressure Gauge

Reading (psi)

Control, No

Joint

Control,

Joint

MC-2010MN Synko-flex

10:00 0 20.3 19 17.2 17.5

10:35 5 24.5 23.5 22.1 48.5 *

11:05 10 27.4 26.7 25 N.A.

11:35 15 29.4 28.9 27.2 N.A.

12:00 20 31.8 31.8 29.5 N.A.

12:30 25 33.8 37.3 31.2 N.A.

1:00 30 36 52 * 33.2 N.A.

1:30 35 38 54 35 N.A.

2:00 40 40.3 56.3 37 N.A.

2:30 50 44.2 N.A. 39.8 N.A.

3:00 60 47.8 N.A. 43.2 N.A.

3:30 70 51 67.4 46.4 N.A.

4:30 80 55.8 73.4 48.6 N.A.

5:00 90 N.A. 82.3 52.5 N.A.

5:30 100 77 87.5 55.6 N.A.

* Pressure system leak observed.

217

B2. - Water volume changes – second experiment – stage one.

Volume Changes (cm

3

)

Specimen

A1 B1 C1 D1

Time

Air Pressure

Gauge Reading

(psi)

Control,

No Joint

Control,

Joint

MC-2010MN

Synko-flex

10:00 0 0 0 0 0

10:35 5 532.0 570.0 620.7 3927.0

11:05 10 899.4 975.4 988.1

11:35 15 1152.8 1254.1 1266.8

12:00 20 1456.8 1621.5 1558.1

12:30 25 1710.1 2318.2 1773.5

1:00 30 1988.8 4180.3 2026.8

1:30 35 2242.2 4433.7 2254.8

2:00 40 2533.5 4725.0 2508.2

2:30 50 3027.6 2862.9

3:00 60 3483.6 3293.6

3:30 70 3889.0 3699.0

4:30 80 4497.0 3977.7

5:00 90 4471.7

5:30 100 4864.4

218

B3. - Water level changes – second experiment – stage two.

B4. - Water volume changes – second experiment - stage two.

Volume Decrease (cm

3

)

A

2

:

0

2

:

1

0

2

4

8

2

:

3

7

Water Column Height (cm)

T

i

m

e

A

2



B

1

:

5

0

2

:

0

2

1

.

2

:

1

0

3

0

.

3

2

:

2

0

4

0

.

4

2

:

3

0

5

3

.

2

:

4

0

2

:

5

0

N

.

A

.

3

:

1

0

N

.

A

.

3

:

2

0

N

.

A

.

3

:

3

0

N

.

A

.

3

:

4

0

* Pressure system leak observed.

219

2

:

3

0

5

3

8

3

2

:

7

4

2

:

5

0



4

7

3

:

1

0



5

3

:

2

0

3

:

3

0



3

:

4

0



B5. - Water volume losses – second experiment – stage three

Water Level Changes

Mortar / Slurry-- Top Pour

Tegraproof

D3 F3 Total Lost (g)

Volume Lost

Total Lost (g)

Volume Lost

T

i

m

e

S

l

u

r

9

:

2

7

1

5

.

3

9

:

3

0

9

:

3

5

3

5

.

6

9

:

4

0

4

7

.

1

9

:

4

5

.

7

9

:

5

0

N

.

A

.

9

:

5

N

.

A

.

1

0

:

2

5

1

0

:

5

N

.

A

.



1

:

2

5

N

.

A

.



1

:

5

N

.

A

.



1

2

:

2

5

N

.

A

.



1

2

:

3

0

N

.

A

.



1

2

:

3

5

1

2

:

4

5

N

.

A

.



1

:

0

N

.

A

.

1

:

3

0

N

.

A

.

1

:

3

5

N

.

A

.

1

:

4

5

N

.

A

.

2

:

0

2

:

3

0

N

.

A

.

3

:

3

5

N

.

A

.

2

:

4

5

N

.

A

.

3

:

0

N

.

A

.

3

:

3

0

220

APPENDIX C

EXPERIMENT 3

C1. - Waterstop-RX 101TRH - specimen one.

C2. - Waterstop-RX 101TRH - specimen two.

Waterstop RX-2

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

0

2

0

1

C3. - Waterstop-RX 101TRH - specimen three.

Waterstop RX-3

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

1

9

1

3

2

8

2

5

Waterstop RX-1

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

(

D

a

y

)

(

m

)



0

1

2

35

7

221

C4. - Waterstop-RX 101TRH - averages.

Waterstop RX-AVG

Time Weight Length Thickness

Width

Expansion

Rate

Thickness

Increase

(Day) (g) (mm) (mm) (mm) (%) (mm)

0 156.5 198.7 17.7 25.9 0.0 0.0

1 275.0 229.5 27.2 39.3 75.7 9.5

3 394.4 186.3 34.0 48.4 151.9 16.4

5 481.2 220.0 42.0 55.8 207.4 24.4

7 525.3 116.3 42.3 59.3 235.6 25.0

222

C5. - MC-2010MN – specimen one.

MC 2010-MN-1

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

(

D

0

2

1

3

2

0

5

2

0

2

0

1

4

1

2

0

2

8

2

0

3

1

2

0

3

4

2

0

C6. - MC-2010MN – specimen two.

MC 2010-MN-2

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

(

D

0

2

0

1

2

0

3

5

2

0

1

0

2

0

223

1

2

1

2

0

2

3

6

4

2

C7. - MC-2010MN – specimen three.

MC 2010-MN-3

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

(

D

0

2

1

3

5

2

0

1

4

1

2

8

3

2

3

4

2

1

224

C8. - MC-2010MN – averages.

MC-2010MN-AVG

Time Weight Length Thickness

Width

Expansion

Rate

Thickness

Increase

(Day) (g) (mm) (mm) (mm) (%) (mm)

0 23.4 200.0 9.0 15.0 0.0 0.0

1 28.5 202.3 10.7 16.8 21.7 1.7

3 32.3 204.5 11.5 17.3 37.9 2.5

5 34.8 205.7 11.7 17.7 48.6 2.7

7 37.0 206.3 12.1 17.9 57.8 3.1

10 39.5 208.0 12.2 18.0 68.3 3.2

14 41.8 208.3 12.4 18.0 78.5 3.4

15 42.4 208.3 12.6 18.0 80.7 3.6

20 45.0 208.7 12.6 18.0 91.9 3.6

28 48.0 208.7 12.6 18.0 104.7 3.6

31 48.2 208.7 12.6 18.0 105.7 3.6

36 48.6 208.7 12.7 18.0 107.5 3.7

42 48.7 208.7 12.7 18.0 108.0 3.7

225

C9. - Synko-Flex – specimen one.

Synko-Flex-1

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

(

D

(

m

0

1

2

0

3

5

2

1

2

1

4

2

1

2

0

2

1

2

8

3

1

2

1

3

4

2

1

C10. - Synko-Flex – specimen two.

226

Synko-Flex-2

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

(

D

0

2

0

1

3

2

0

5

2

0

1

4

1

5

2

0

2

0

2

8

2

0

3

2

3

6

4

2

0

C11. - Sykno-Flex – specimen three.

Synko-Flex-3

Time

Weight

Length

Thickness (mm) Width (mm)

Expansion

Rate

Thickness

Increase

(

D

0

1

9

1

2

3

5

2

0

1

0

2

0

227

1

4

2

0

1

5

2

0

2

0

2

0

4

2

0

C12. - Synko-Flex – averages.

Synko-Flex-AVG

Time Weight Length Thickness

Width

Expansion

Rate

Thickness

Increase

(Day) (g) (mm) (mm) (mm) (%) (mm)

0 156.6 200.0 16.9 33.7 0.0 0.0

228

1 157.1 204.3 17.4 34.1 0.3 0.5

3 157.3 206.0 17.7 33.6 0.5 0.7

5 157.6 206.0 17.7 33.7 0.6 0.8

7 157.5 206.0 17.7 33.9 0.6 0.8

10 157.9 206.3 18.0 33.9 0.8 1.1

14 158.2 207.0 18.1 33.9 1.0 1.1

15 158.2 207.0 18.1 33.9 1.0 1.1

20 158.5 207.3 18.1 33.9 1.2 1.1

28 158.8 207.7 18.1 33.9 1.4 1.1

31 158.8 208.0 18.1 33.9 1.4 1.1

36 159.1 208.7 18.1 33.9 1.6 1.1

42 159.4 208.7 18.1 33.9 1.8 1.1