DASA 2698 July 1971 UNCLASSIFIED TRIAXIAL TESTS ON LARGE ... · Principal Investigator and Madan M....
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DASA 2698 July 1971
UNCLASSIFIED
TRIAXIAL TESTS ON LARGE ROCK SPECIMENS
by
Peter Jay Huck
Madan M. Singh
for
HEADQUARTERS Defense Atomic Support Agency
Washington» D.C. 20305 'r-
IIT RESEARCH INSTITUTE Technology Center
Chicago, Illinois 60616
SfP 8 t97t
Contract No. DASA01-69-C-0134
■
■
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"Approved for Public Release; Distribution Unlimited"
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unciassmea 3«-:r.v C'.i^«-.'';: •••.'-! w^
1 DCCUMsNT CONTROL DATA- R i 0 ■»*'
Unclassified ill Research Institute, Chicago, Illinois ^ »"^
It. «tPOWT TITLE
TRIAXIAL TESTS ON LARGE ROCK SPECI>ENS
4. OtlC«t»Tive KOJtt Tvp* ol upon ami inclutii» i»t*t)
Draft Final Report No. D605''-23 S- AUTHOR.*'frirtr r<n«, T.IMI» inmtl. IM»I narr»)
Peter J. Huck and Madan M. Singh
«. noo«T a* TC
April 1971 T«, TOTAL S3. O* PASEt 76. NO. of men
165 45 »*. OXISINATSa'S RE»0»T NUMSEKISI
DASA 2698
DASA-01-69-C-0134 b. rnojtcT HO
AREA Order Number 1397
Progr.au. Code 9F10 »A. OTHC« nevanr NOISI (Any oth»t numt>»rt thai may d« mttiinfi
thl* np»tt)
IS. OiSTAiauTiON »-»rävcNT
Approved for public release, distribution unlimited
It. S*ONSOaiN6 MIUITAMV ACTIVITV
Director, Advanced Research Project Agency, 1400 Wilson Blvd., Arlingt< Virginia 22209
f A A studv was conducted to determine the effect of specimen size
on the mechanical response of rock. Specimens of Cedar City tonalite (Cedar City, Utah) and Charcoal Black granite (Cold Springs, Minnesota ranging in size from 2 in. dta. to 32 in. dta. (24 in. dia. for the tonalite) were tested in triaxial compression. In addition to the standard triaxial test stress trajectory, one specimen of each rock type was loaded unt^xial strain to simulate true one-dimensional compression. Test data Included axial and circumferential strain at up to 30 locations on the largest specimens, surface wires to indicate crack propagation on the 12 inch and larger specimens, axial and radial stresses and the confining pressure media temperature. Data were recorded under loading, unloading and reloading conditions. The test data for each specimen size and rock type were fit to a non-linea hysteretic model to determine variation In the model parameters as a function of specimen size. / .
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K C • tiOAOi
Large Triaxi-il Tests
Scale Effect;
Cedar Ci.cy Tonal Lee
Charcoal alack Grinice
Non-Linear Hyscerecic Model
■»JL-;! IT ^3i.3 «■ | o L ? 1 A'
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Details of Illustrations tn^s this document may be better
studied on microfiche
IITRI Project No. D6051 Final Report No. D6051-23
Contract No. DASA-01-69-C-0134
TRIAXIAL TESTS ON LARGE ROCK SPECIMENS
by
Peter Jay Huck Madan M. Singh
for
Department of Defense Advanced Research Projects Agency
Washington, D.C.
July 1971
The views and conclusions contained In this document are those of the authors and should not be Interpreted as neces- sarily representing the official policies, either expressed or Implied, of the Advanced Research Projects Agency or the U. S. Government.
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DASA 2698
TRIAXIAL TESTS ON LARGE ROCK SPECIMENS
by
Peter Jay Huck
Madan M. Singh
IIT Research Institute
Technology Center
Chicago, Illinois 60616
ARPA Order Number ARPA 1397 Program Code Number 9F10 Name of Contractor IIT Research Institute Effective Date of Contract 15 May 1969 Contract Expiration Date 15 Aug 1971 Amount of Contract $ $99,000 Contract Number DASA01-69-C-0134 Principal Investigator and Madan M. Singh
Phone Number AC312/225-9630 Ext. 4784 Project Scientist or Engineer Peter J. Huck
and Phone Number AC312/225-9630 Ext. 4735 Short Title of Work Triaxial Tests Large Rock Specimens
Sponsored by
Advanced Research Projects Agency
ARPA Order No. 1397
The views and conclusions contained in this document are those of the authors and should not be interpreted as necessarily representing the official policies, either expressed or implied, of the Advanced Research Projects Agency or the U.S. Government.
"Approved for public release; distribution unlimited"
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FOREWORD
This is a final report on IIT Research Institute (IITRI)
Project D6051 (IITRI Report No. D6051-23) entitled, "Triaxial
Tests on Large Rock Specimens". This research was supported
by the Advanced Research Projects Agency of the Department
of Defense and was monitored by Mr. Clifton McFarland under
Contract No. DASA 01-69-C-0134.
The project was conducted under the supervision of
Dr. Madan M. Singh, who served as program manager. Mr. Peter
J. Huck was project engineer. Other IITRI staff members who
contributed to the overall research effort include Dr. R. H.
Cornish and Messrs. F. W. Dew, L. A. Finlayson, P. A. Hettich,
S. Martin, R. D. Nelson and J. J. Vosatka.
Respectfully submitted,
IIT Research Institute
/ 4 Py y^L^l Peter Jay Huck Project Engineer
APPROVED:
R. H. Cornish Director Mechanics of Materials Division
PJHrbk
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TABLE OF CONTENTS
Section Page
1 INTRODUCTION 2
2 PREVIOUS STUDIES ^
2.1 Effect of Size 4
2.2 Effect of Confinement 7
3 EXPERIMENTAL APPARATUS 9
3.1 Small Test Cells 11
3.2 48-Inch Test Cell 11
3.3 Specimen Preparation 17
3.4 Instrumentation and Data Reduction 18
4 EXPERIMENTAL PROGRAM 21
5 DISCUSSION OF RESULTS 30
5.1 Theoretical Considerations for 30
Constitutive Equations
5.1.1 Formulation of Constitutive 30
Equations
5.1.2 Limit Surface 31
5.1.3 Elastic Equations 33
5.2 Typical Behavior of Rock 34
5.2.1 Hydrostatic Behavior 34
5.2.2 Triaxial Compression 39
5.2.3 Uniaxial Strain 43
5.2.4 Poisson's Ratio and Young's 43
Modulus
5.2.5 Yield and Fracture Criteria 45
5.3 Analysis of Experimental Results 47
5.3.1 Charcoal Black Granite 47
5.3.2 Cedar City Tonalite 59
5.3.3 Uniaxial Strain Tests 66
5.4 Strength Properties 72
6 SUMMARY AND CONCLUSIONS 74
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TABLE OF CONTENTS (Cont'd.)
Section Page
REFERENCES 78
APPENDIX A - COMPUTER PLOTS OF TEST DATA A-l
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LIST OF FIGURES
Figure Page
1 Typical Triaxlal Cell Schematic 10
2 Schematic of System for 2 in., 4 in., and 12 12 in. Triaxial Specimens
3 48 in. dia. Cell with 32 in. dia. Specimen 13 Being Loaded
4 Schematic of 48 in. dia, Triaxial Cell 14
3 Radial Strain Gages for Uniaxial Strain Tests 16
6 Typical Gage Layout 15
7 Loading Specimen Into 48 in. dia. Triaxial 23 Cell
8 Inserting Sliding Piston Into 48 in. dia. 24 Triaxial Cell
9 Removing Fractured Specimen From 48 in. 25 dia. Triaxial Cell
10 32 in. dia. Charcoal Black Granite Specimen 26 After Tests 27-28 (oc - 5000 psi)
11 32 in. dia. Charcoal Black Granite Specimen 27 After Tests 29-30 (ac - 10,000 psi)
12 32 in. dia. Charcoal Black Granite Specimen 28 After Test 31 (uniaxial strain)
13 22 in. dia. Cedar City Tonalite Specimen 29 After Test 32 (uniaxial strain)
14 Yield Surface for Mises' Yield Criterion 32
15 Typical Compressibility Curve for Rock, 35 After Paulding (40)
16 Compressibility of Granite, Gabbros and 36 Diabases, After Clark (41)
17 Stress Strain Curve for Nonlinear Hysteretic 38 Model
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LIST OF FIGURES (Cont'd.)
Figure Page
18 Idealized Stress Strain Behavior of Rock 41 After Swanson (21)
i
19 Variation of Shear Modulus with Mean Stress 42
20 Yield Criteria 46
21 Mean Stress vs. Volumetric Strain, Typical 48 Response for Charcoal Black Granite
22 Bulk Modulus vs. Mean Stress - 2" 0 and 4" 0 49 CBG
23 Bulk Modulus vs. Mean Stress - 12" 0 and 32" 0 50 CBG
24 Devlator Stress vs. Strain, Charcoal Blick 54 Granite
25 Tangent Moduli for Charcoal Black Granite, 55 2-In. Dla.
26 Tangent Moduli for Charcoal Black Granite, 56 4-In. Dla.
27 Tangent Moduli for Charcoal Black Granite, 57 12-In. Dla.
J
28 Tangent Moduli for Charcoal Black Granite, 58 32-In. Dla.
29 Polsson's Ratio vs. Mean Stress for 2" 0 61 and 4" 0 Charcoal Black Granite
30 Polsson's Ratio vs. Mean Stress for 12" 0 62 Charcoal Black Granite
i
31 Polsson's Ratio vs. Mean Stress for 32" 0 62 Charcoal Black Granite
32 Bulk Modulus for 2" Cedar City Tonailte 63
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Figure
33
34
LIST OF FIGURES (Cont'd.)
Page
Bulk Modulus for 4" Cedar City Tonalite 63
Variation of Bulk Modulus for Cedar City 64 Tonalite, 2-in., 4-in. and 12-in. dia.
35 Volumetric Strain for Cedar City Tonalite 64 Models
36 Bulk Modulus for Cedar City Tonalite Models 65
37 Tangent Moduli for Cedar City Tonalite 67
38 Poisson's Ratio for Cedar City Tonalite 68
39 Uniaxial Strain Test 70
40 Shear Behavior for Uniaxial Strain Tests 71
41 Volumetric Strain for Uniaxial Test 71
42 Maximum Value of VjJ" Reached for All 'rests 73
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ABSTRACT
A study was conducted to determine the effect of
specimen size on the mechanical response of rock« Specimens
of Cedar City tonalite (Cedar City, Utah) and Charcoal Black
granite (Cold Springs, Minnesota) ranging in size from 2 in,
dia. to 32 in. dia. (22 in. dia. for the tonalite) were tested
in triaxial compression. In addition to the standard triaxial
test stress trajectory, one specimen of each rock type was
loaded under uniaxial strain to simulate true one-dimensional
compression. Test data included axial and circumferential
strain at up to 30 locations on the largest specimens, surface
wires to indicate crack propagation on the 12 inch and larger
specimens, axial and radial stresses and the confining pressure
media temperature. Data were recorded under loading, unloading
and reloading conditions. The test data for each specimen
size and rock type were fit to a non-linear hysteretic model
to determine variation in the model parameters as a function
of specimen size.
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TRIAXIAL TESTS ON LARGE ROCK SPECIMENS
1. INTRODUCTION
Currently a number of structures are being located 1 2 underground, many of which are in rock. It is anticipated *
that the number of such underground structures will increase
enormously in the next two decades. It may be concluded that
the number of structures in rock will increase correspondingly.
In spite of this anticipated underground construction activity,
little is known about the mass behavior of rock. It is
qualitatively recognized, of course, that the rock mass behaves
distinctly differently from the matrix in small samples, but
this effect of size is not well understood, and cannot be
predicted, to date, with any degree of confidence. These
variations are attributed to joints and other weakness planes
in the rock mass. Yet, most of the test procedures for
determining strength and elastic moduli information about
rocks are based on these properties on small samples .
It is both difficult and expensive to try to perform properties
tests on larger specimens. Hence some relationships between
the various sizes need to be established. It was the intent
of this program, to study the mechanical behavior of rock
specimens of different sizes, and to determine how these
relate to each other.
During this program, two varieties of rock. Charcoal
Black granite from Cold Springs, Minnesota and Cedar City
tonalite from Cedar City, Utah, were investigated. Four
sizes of rock cores, 2-in. dia., 4-in. dia. 12-in. dia.,
and 32-in. dia. (22-in. in case of the tonalite) were subjected
to triaxial compression tests. The specimens were strain
gaged to determine the elastic moduli!. One test, on the
large core samples of each rock type was uniaxial strain
only. The data obtained was correlated to ascertain trends.
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Accumulation of sufficient data on size effects
with various rock types may be expected to finally lead
to predictive equations for the rock mass. It should be
borne In mind, however, that the strength properties of smaller
rock samples are governed by mlcroflaws such as crystal
lattice disturbances, grain boundaries, minute voids (pores)
and weak cementing material. The strength of the rock mass
Is dependent on macroflaws, I.e. failure planes, joints,
cavities, and Intrusions. It also appears probable that
the rock mass Is more affected by environmental conditions
than the matrix. In general, environmental factors Induce
a time-dependent reduction In strength by chemical alteration,
rheologlcal deformation, and structural failure. The roles
of residual stresses In the rock matrix and erogenic forces
on the mass are not well understood; hence their effect on
rock, behavior requires further study. The presence of water
significantly affects the behavior of the rock mass as well
as the matrix. In general It tends to reduce the structural
strength, but whether the manner In which this Is accomplished
In the two cases Is the same, has not been clearly established.
Finally, It should be mentioned that the configuration of
the rock mass, and the base material on which It rests probably
controls Its gross behavior. It would be difficult to simulate
these conditions In laboratory samples, but the overall effects
maybe estimated by varying size and end conditions.
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2, PREVIOUS STUDIES
2.1 Effect of Size
Several studies have been conducted to determine the
effect of size of specimens. Most of these have been with
unconflned compresslve tests. Rice and Enzian showed that
the compresslve strength of 2 1/2 - 4 In. coal cubes was about
2500 psl, whereas a 54 In. cube of the same coal failed at o
300 psl. Greenwald, Howard, and Hartmann related the size
of coal pillars to their compresslve strength at an experimental
face by over-cutting and side-cutting. There was a decrease
In strength with increasing pillar height relative to the
cross-sectional area, the breaking stress o for small pillars
approximately satisfying the relationship
,bv0.5 aco< (*) ,
where b is the lateral dimension of the pillar and h is its
height. Burton and Phillips9 studied the relationship between
size and compresslve strength of cubes of anthracite over the
range 1/4 in. to 4 in. and found that
a Pc a-0.45+0,05 c »
where a is the linear dimension of the cubes. Millard, Newman 10
and Phillips extended the range of these observations, and
used Griffith's theory of crack propagation to explain the
failure phenomenon. Both these investigations by Phillips and
his associates may be said to show that approximately
oc<* a"0'5,
Evans and Pomeroy 1 found that the relation between the mean
crushing load (9) and the side of the cube (a) Is'of the
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form <poc aß,
where ß - constant varies between 1.5 and 2, I.e.,
-0.5 to 0 a oc a c
Holland12 has suggested a coal pillar design formula as
follows: ka0'5
where a - least width of pillar (Inches)» h - thickness of
pillars (Inches), and k - coefficient depending on type
of coal. This Is valid for a/h ratios between 1 and 10.
For rocks, the types of relationships developed are
slightly different. According to the Welbull theory ,
(f )" - CS) m v
where o - tensile or compressIve strength of the rock from a
standard laboratory test,
ü ■ equivalent strength of the rock mass,
v - volume of the rock mass,
v « volume of the test sample, and
00 - constant (with values near 10 for rocks).
The relation established by Protodyakonov was of the type
2». i + «(*- 1) am 8 + *
where s - spacing between major discontinuities In the rock
mass, e.g., joints, beds,
a - dimension of the test specimen, usually diameter
for compression tests, and
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K - mass fracture coefficient (in compression:1-2 for
igneous rocks, 1-3 for competent sedimentary
rocks, 3-iO for weak rocks; in tension: approximately
double these values).
Grobbelaar , based on the work of Epstein , Bieniawski ,
and others, found that the formulae relating the modal
strength of the weakest elements and its standard deviation,
based on the weakest link theory, are
oN - au - o8 (21ogN)0'5- 1/2 [log(logN) + log(4 )} (21ogN)"0-5
and a (N) - oa xir(121ogN)'0,5
8 8
or as(N) - as(N0) (logN0/logN)0-5
where N - number of flaws in the large cubic specimen,
■ number of unit cube.
N - number of flaws in the small cubic specimen or
Oj, - modal strength of the weakest link in a sample
containing N elements,
a - average strength of a unit cube of material
containing N elements.
og - standard deviation of the modal strength of
samples containing N elements,
and 08(N) - standard deviation of the modal strength
of the weakest element in a sample containing
N elements.
These formulae are based on the "weakest link theory",
which can be analyzed mathematically if it is assumed that
the frequency of occurrence of events is a continuous
function (e.g. Weibull13 or normal distribution). The "links"
in this case are the macroflaws (or cracks) in the bulk
material; not the microflaws.
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18 19 Glücklich and Cohen » have indicated that effects
other than statistical exist, since the total stored elastic
energy increases with specimen volume. The energy released
at onset of fracture is related to initiate fracture; in other
words, this reduces the rock strength. This phenomenon has
been recently discussed by Baecher .
2.2 Effect of Confinement
There have been numerous studies investigating the
effects of various aspects of confinement on rocks. It is
not intended to review all of these completely in this section.
Most of the pertinent work has been briefly discussed by 21 Swanson , The earliest experimental work was performed by
22 23 Adams and von Karman . However, significant headway was
24 not made until the initiation of work by Griggs and
2*1-26 his coworkers . Since then a number of
researchers have conducted various types of studies under
pressure several of which were presented at a symposium on
rock deformation . Baidyuk has summarized some of the
Russian and American work. Research in this area is still 21 29 30
very active * * . All of this work has been performed
with small rock specimens, a few inches in diameter. As a
result considerable light has been shed on the behavior of
the rock matrix and the criteria of failure. Refinements
to the Griffith hypothesis have been proposed 33 and
appear to explain the rock fracture process under confinement
fairly well. The extrapolation of these theories to larger
rock masses is of doubtful value and hence large scale
field testing has to be resorted to . The U. S. Bureau of
Mines has undertaken a rather comprehensive program to
collect field data with the intention of correlating it into
a hypothesis 5. The contributions of Hoek36, Bieniawskl37.
Cook , Wawersik-'0 and Houpert"" to the mechanism of brittle
failure in rock deserve to be noted even though the studies
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were not conducted under a confined state of stress.
To the best of the authors' knowledge no experimental
Investigations on large rock samples under confinement have been performed.
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3. EXPERIMENTAL APPARATUS
In order to conduct triaxlal tests for the range of
specimen sizes used on this project, four triaxial cells
were set up as shown below:
Chamber I.D. (in.)
Specimen Diameter (in.)
Maximum Chamber Pressure
(ksi)
Maximum Axial Load lb. x 10°
4.0 2.06 30 0.375
6.5 3.65 30 0.990
14.7 10-12 20 3.40
48.3 22-32 20 axial 10 confining
36.5
In a standard triaxial cell the axial load is supplied by an
external loading machine. However, in order to achieve the
large end loads required for the tests in this program, these
chambers were separated into two regions by sliding pistons.
The general configuration is shown in Fig. 1. One region
contained the specimen, and was pressurized to the desired
confining pressure. Axial load was transmitted to the rock
by the sliding piston. The maximum axial stress in the rock
depends upon the ratio of the rock and piston areas and the
difference in the confining pressure and the axial chamber
pressure. The specimen stresses are given by the following
equations:
where
a2 - 03 - P3
Affl " <VP3> Xf al - ^3 + Aal
A • piston area
Ar - specimen area
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Chamber Closure with Instrumentation Lead- Out
Confining Pressure Region
Test Specimen
Sliding Piston with Loading Blocks
Axial Pressure Region
Fig. 1 TYPICAL TRIAXIAL CELL SCHEMATIC
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P* * axial chamber pressure
Fo ■■confining chamber pressure
Acr, - deiviator stress
a-, a« and ö- "principal stresses.
Reference to Figure 1 and the above equations confirms that ' if P, ■ F~, Atfj « 0 and the specimen is uhder hydrostatic stress (<J, " a2 m a^' ^or P3 " ®* t:^e 8Pec:^men ^8 unconfined, with eg - a3 - 0 and ^ - AO^ - V^ A /Ar. ' '
3.1 Small Test Cells i
The three smaller test cells are Incorporated into a testing system with centralized controls, instrumentation, and pumping systems. A schematic of this system is shown in Fig. 2. The tests conducted in this system consisted of initial hydrostatic loading up to the desiredj conflnlhg pressure, followed by triaxial compression at constant p* above that pressure. At least one load-unload-reload cycle was observed for each test. Provision was made for pressure cross-connections between the'confining pressure and axial pressure chamber volumes to Insure hydrostatic conditions during the hydrostatic test phases.
3.2 48^Inch Test Cell ) ■ ^ — ■ i •
This test cell is shown in Figs. 3 aiid 4. The basic unit is a 48" I.D. by 86" working length,chamber having ' 20,000 psi design working pressure. The chamber walls are built up from rings 12" long which are held in place by a 3/4" thick liner on the inside diameter. The entire axial load is carried by a flexible reaction frame which was built up from steel strap. The l40 ton weight of this' chamber is substantially less than the weight that would have been required by conventional chamber design. This is the
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3!
»
M
CM
z M
M
CM
i CO
CO
fa o ÜCO MZ EH
WÜ
U fa COCO
CM
00 •l-l fa
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NOT REPRODUCIBLE
Fig. 3 48 IN. DIA. CELL WITH 32 IN. DIA. SPECIMEN BEING LOADED
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3
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largest chamber currently available at IIT Research Institute,
and is capable of applying axial loads of 36 million pounds
to rock specimens as large as 3 1/2 ft. in diameter.
As can be seen in the schematic, the pumping
and control systems for this unit are simpler than for
the small chambers. A separate pump was used at each end
of the chamber. Accumulators were not used because the
chamber volume itself is large in comparison with other
available pressure chambers.
The operation of this chamber is similar to that
of the smaller chambers, except that the turn-around time
between tests in on the order of a week instead of an hour.
The tests in this chamber differed slightly from those in
the smaller test cells. In order to maintain seal integrity,
a positive pressure differential of about 200 psi was maintained
across the sliding piston during the "hydrostatic" portions
of the triaxial tests, and the axial pressure was not allowed
to drop below 400 psi at the bottom of the load-unload-reload
cycle. Had these precautions not been taken, there would
have been danger of upsetting the piston seal, thus aborting the remainder of the test.
TWo of the large specimens were loaded to produce
unlaxial strain. Figure 5 shows the two transducers were
designed to provide measurements of average radial strain.
One transducer consisted of a full strain gage bridge using
manganin wire elements. The active elements each consisted
of 4 turns of manganin wire wound tightly around, but not
bonded to, the specimen. Temperature and pressure compensation
were achieved by similar elements loosely wound on the
specimen next to the active elements. The second transducer
consisted of an open steel loop pinned to the specimen.
The open ends of the loop were Jointed by a flexible strap
mounting foil strain gages as shown in Figure 5b. Small
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Active Elements
Passive Elements
5a - Manganln Wire Gages
Strain Gages on Flex Strap
Contact Points
5b Beam Type Gage
Fi8* 5 !ESTSL STRAIN
GAGES F0R UNIAXIAL STRAIN
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deflections at the diametrically opposed pins cause relatively large bending strains In the flexible strap. This transducer suffered from somewhat erratic operation, as Is usual with any point-to-point gages on rock specimens.
3.3 Specimen Preparation
Specimens of the Charcoal Black Granite were bought from Cold Spring Granite Co. In Cold Spring, Minnesota, but the Cedar City tonallte was supplied by DASA. In both cases, the larger cores (10 or 12-ln. and 22 or 32-ln. dla.) were obtained as such from the source, but the 2-in. and 4-in. dla. specimens were cored In the laboratory from extra rock obtained In each case. These smaller cores were cut parallel to the axis of the larger cores so as not to Introduce complications because of anlsotropy.
End preparation of the 2-ln. and 4-in. dla. cores consisted of facing on a lathe until the ends were plane and parallel to 0.001 inches. The larger cores were capped in a specimen cage to permit handling. The capping material used was a steel-filled epoxy. Figures 3 and 7 each show an assembled 32 inch specimen in its cage. The cage tie rods were designed with end fittings that would accept tensile load only. Since the maximum tensile load that could be applied to the cage by these tie rods corresponded to 30 psi compressive stress in the rock specimen, the effect of the cage on the rock was negligible.
An array of foil strain gages were mounted on each specimen. The number used ranged from three rosettes on the 2 in. cores to thirty rosettes on the 32 in. cores. These were two element rosettes with 1/4 in. gage length placed with the direction of rolling parallel to the specimen axis. The gage placement procedure included the following steps:
* grind the rock surface
* apply two thin coats of gage cement NT RESEARCH INSTITUTE
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* visual Inspection for voids In the cement base * affix and wire gage * apply two coats of gage cement for water proofing * check gage for continuity and response (soft
eraser) and replace If necessary.
In several cases It was necessary to move a rosette slightly away from Its pre-determined location because of local flaws or drill shot embedded in the surface (especially in the case of the tonslite).
In addition to the gages, break wires were cemented to the surface of the 12-in. and greater diameter specimens. This wire was No. 36 manganin wire well bonded to the surface so that the wire would break if a crack propagated across it during a test. Figure 6 shows typical instrumentation for a 12-in. core.
The Instrumented cores were waterproofed with latex cement over the foil gages, and at least two coats of latex paint with a thickening agent spread over the entire rock surface. Waterproofing is very important in a triaxial test since both the loading conditions and the character of the rock can be changed by intrusion of oil into the rock voids. In those tests where the specimens could not be loaded to failure on the second load cycle, the specimen was recovered intact and stripped of paint for visual inspection. In several cases, traces of oil were found under the paint, but typically the specimens were completely dry. In no case was there enough oil to do more than dampen a very small area on the specimen surface.
3.4 Instrumentation and Data Reduction
The instrumentation on this program Included foil strain gages, temperature transducers, pressure gages and break wires on the larger specimens. All instrumentation except the pressure gages were recorded using an automatic
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Axial Surface Wire
Circumferential Surface Wir<
Foil Strain Gage Rosettes In 4 x 6 Matrix
Fig. 6 TYPICAL GAGE LAYOUT
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data acquisition system. The pressures were read using
Hiese Super Accurate bourdon gages and inserted manually
onto the data system output as they were read.
Due to the bulk of data involved, the data were
reduced and plotted using the 1108 Univac computer at IITRI.
In addition to printed output, the following plots were
produced for each test:
Shear strain vs. deviator stress
Volumetric strain vs. mean stress
Poisson's ratio vs. mean stress
Octahedral shear stress vs. mean stress
Circumferential and axial strain vs. axial
stress
Elastic, shear and bulk moduli vs. mean stress.
Data from each test was then assembled by hand to show trends
from test to test.
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4. EXPERIMENTAL PROGRAM
The program included trlaxlal tests on specimens
ranging from 2-in. to 32-in. dia. One uniaxial stiain test
was conducted on the largest available specimen for each
rock type, these being a 32-in. dia. granite and a 22-in.
dia. tonelite. The uniaxial tests were conducted by monitoring
mean radial strain and maintaining sufficient confining pressure
to hold this strain as near zero as possible. The experiments."V
program is summarized in Table 1. IITRI was able to procure
the granite core from Cold Springs Quarry, Minnesota. The
tonalite specimens were delivered by DASA which was unable
to obtain more than one large specimen of tonalite.
The loading and unloading sequence in the large
chamber is shown by the photographs in Figs. 7, 8 and 9.
Typical failures are seen in Figs. 10 thru 13.
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f-l X) (0 H
<
I H OL W
X w
H
r-l \ / \ / \ / \ 1 Iw v 1 CD C \ / \ / \ / \ 1 \ / \ / •rl*H \ / \ / \ / \ 1 \ / \ / X CD \/ \/ \ / H \l \/ \ / «N CD U v v v CO Y Y Y CO
■M 4J X X x A A \
lM A A A A A A >H i w \/ CO
\ / \ / CO \ / \/ CM \ / \ / Ü •4- ON y x CO
CO <M y y 0 m A A CM /\ i\
o H /\ /\ / \ I \ 0) / \ / \ / \ / \ Vi / \ f \ / \ / \ 3 f '. f \ 10 y / (0 \ / 0) •H o \ / M so CO \ / S * <t ^ o 1 *o 00 00 \j
<-4 l-< H ON CM l-l CO i Y M) a M f\ Ö M I \ i-l / \ C1 / \
C / ' \ \ / 0 « \ /
Ü ^H r-l 00 m sO \ / « fM <M «M CO v J* ^ ON •|>. 1 « 9k r*. x
T-l von r* ^i- m H A »n H <N «N' CO /\
1 /, \
<u •
i
.
; 1
h 5 <NJ <t <N CM fS St <N CM 0»^ H co j H CM UQ /
l-l CD «
i I O 4J ' »J '
Rock
Type
Chare
Black
Grant
i Cedar
City
Tona
l:
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NOT REPRODUCIBLE
Fig. 7 LOADING SPECIMEN INTO 48rINJ DIA. TRIAXIAL CELL
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NOT REPRODUCIBLE
Fi8' 8 Tmx™GCELLDING PIST0N INT0 48-IN- DIA-
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NOT REPRODUClBLE
Fig. 9 REMOVING FRACTURED SPECIMEN FROM 48-IN. DIA. TRIAXIAL CELL
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NOT REPRODUCIBLE
Flg. 10 32-IN. DIA. CHARCOAL BLACK GRANITE SPECIMEN AFTER TESTS 27-28 (ac - 5000 psi)
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NOT REPRODUCIBLE
Fig. 11 32-IN. DIA. CHARCOAL BLACK GRANITE SPECIMEN AFTER TESTS 29-30 (ae - 10,000 psi)
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NOT REPRODUCIBLE
Fig. 12 32-IN. DIA. CHARCOAL BLACK GRANITE SPECIMEN AFTER TEST 31 (UNIAXIAL STRAIN)
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NOT REPRODUCIBLE
Flg. 13 22-IN. DIA. CEDAR CITY TONALITE SPECIMEN AFTER TEST 32 (UNIAXIAL STRAIN)
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5. DISCUSSION OF RESULTS
5,1 Theoretical Considerations for Constitutive Equations
The large amount of data generated during this program
makes a simple report of experimental data inappropriate.
The reduced data itself consists of an 8 1/2 inch thick stack
of printed computer output. Since it was obvious at the
start of the program that this would be the case, parallel
computer output in the form of graphical plots was provided
for inclusion in the report as an appendix. In order to
summarize the data for discussion in the text of the report,
it was felt that the most convenient form would be a comparison
of the test data with a model. The model parameters can
eben be evaluated as a function of specimen size much more
easily than the actual data.
5.1.1 Formulation of Constitutive Equations
Concepts from the theory of plasticity have recently
been used to describe the behavior of particulate materials
such as soil and rock. If a stress space is constructed with
coordinate axes representing the three principal stresses,
the state of stress of an element of material is described by
a point in this stress space. The locus of all possible stress
states which cause yielding of the material is a surface called
the yield or limit surface. This surface separates the
stress states attainable in the material from those which are
not attainable. An elastic-plastic material is one which
behaves as an elastic material at stress states within the
limit surface, and as a plastic material at stress states on
the limit surface. A material model thus must Include both
a description of the limit surface and the elastic equations
that hold within the limit surface.
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5.1.2 Limit Surface
The limit surface in principal stress space is usually
expressed by
iJf - f(Jj.) (i) In which J, is the first invariant of tbi stress tensor and
JX is the second invariant of the deviatoric stress tensor. These invariants are defined by
Ji (a^a^2 + (al - a2)2 + (a2 - a3)
2
(2)
(3)
in which o-,, ar^i and a- are the three principal stresses. An
equivalent method of describing the yield surface is to write the octahedral shear stress, T tj as a function of the octahedral
normal stress, ou«*-» or
in which
and
W - f(aoct)
ffoct - T <al + a2 + ö3>
koct 1 7 (ol-a2)2 + (a1-a3>
2 + (a2-a3)2
(4)
(5)
1/2 (6)
One form of a yield surface commonly used is the
Mises1 yield criteria given by
J2 - Ko (7)
in which K0 is the yield limit of the material in simple shear.
Equation (7) describes the surface of a cylinder in principal
stress space with the axis inclined equally to all three
principal stress axes as shown in Fig. 14. According to Mises*
yield criterion the shear strength of a material is independent
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Radius V2 K.
Total Stress Vector Vector /-v
Axis of Yield Cylinder
(0! - o2 - 03)
Fig. 14 YIELD SURFACE FOR MISES' YIELD CRITERION
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of the mean stress a , where
In granular materials, Including most soils and rocks, It
has been established that shear strength Increases with
mean stress due to frlctlonal behavior. For these materials
the Coulomb-Mohr yield surface Is more applicable, and Is given
by
VJ]~ - A + B JJ^ (9)
In which A and B are constants. Equation (9) describes the
surface of a cone In principal stress space with the same
axis as the Mlses1 yield criteria shown In Fig. 14.
5.1.3 Elastic Equations
Constitutive equations for an Isotropie linear elastic
material are given by
alj ■ ^ljekk + 2^lj <10>
In which a^. - stress tensor
Ejj - strain tensor
d.j - Kronecker's delta
>%>tl are Lame's constants.
It Is sometimes convenient to separate the volumscrlc response which Is produced by mean stress from the distortion«! response which Is produced by shear stress. This Is accomplished through the devlator strain tensor, e'j4» and the devlator stress tensor, a£., which are defined as
Eij ' eij " T ekk filj <U>
aij " 0lj ■ ? akk 6lj (12)
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The constitutive equations (10) may then be rewritten In the
form , » "a m k 8ij ekk + 2G4j <13)
In which k and G are respectively the bulk modulus and shear
modulus. These moduli are defined by
- a., a- + a« + a0
o-l a»
r1 ' , (l5) e Ij
Nonlinear behavior may be Incorporated by using an Incremental
constitutive relation and defining k and G as functions of
one or more of the stress Invariants. Inelastic behavior
may be Incorporated by using separate values of k and G for
loading and unloading. The unloading moduli must be greater
than the loading moduli to prevent energy generating hystersls
loops.
5.2 Typical Behavior of Rock
5.2.1 Hydrostatic Behavior i
Past work has shown that the stress-strain behavior of rock subjected to hydrostatlq pressure Is non-linear. A
typical curve of mean stress versus volumetric strain from
Pauldiqg Is shown In Figure 15. In an unloaded state a
rock specimen usually has an Initial porosity, Including some
small cracks. As hydrostatic pressure Increases, the cracks
begin to close and the porosity decreases, causing the rock
to become stlffer and less compressible. At higher pressures
the response becomes linear and compressibility of the rock
may be predicted from the Individual compressibilities of
Its constituent minerals. The Initial porosity may be determined
by extending the linear portion of the curve back to the
strain axis. Based on data presented by Clark , shown In
Fig. 16, It appears that the Influence of the Initial
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Compressibility of Solid Material
Volumetric Strain
?ig. 15 TYPICAL COMPRESSIBILITY CURVE FOR ROqC, AFTER PAULDING
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Granites
2Z22ZZZ222ZZ2 Gabbros & Diabases
yzzzzzzzzzzzzzzzzzn
J I I I I I \ I I I L 0 2 4 6 8 10 12
3 Pressure - Bars x 10
Fig. 16 COMPRESSIBILITY OF GRANITE, GABBROS, AND DIABASES; FROM CLARK41
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porosity on compressibility becomes negligible at a pressure
of about 2000 bars or 29 ksi.
The behavior of granular materials under hydrostatic
pressure has been studied analytically through the use of
models consisting of various packings of elastic spheres .
Hertz's contact theory has been used and has shown that
the volumetric strain is directly proportional to mean stress
to the two-thirds power. This nonlinear!ty in response is due
to the geometry of the packing of the individual particles
and not the properties of the material comprising the spheres.
The Hertz theory may be applicable if rock may be considered
as a granular material.
A nonlinear hysteretic model used by Seaman and „44 Whitman to study the behavio..* of sand appears to be suitable
for representing the hydrostatic behavior of rock. The
stress-strain curve for this model is shown in Fig. 17. For
virgin loading
%-*! ** a«) and for unloading and reloading
V - A2 (ev ■ evi in which
° - A9 (e„ - e -)n (17)
a-. " mean stress m
e ■ volumetric strain
e». - residual volumetric strain
A-^ and A2 ■ material properties This model represents both the nonlinear and the Inelastic
behavior of the rock observed under hydrostatic loading.
Application of the mathematical model in a
computer code would perhaps be most convenient in an
incremental form using tangent values of bulk modulus,
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a = A0(f. -e „ ) n
Volumetric Strain, e
Fig. 17 STRESS-STRAIN CURVE FOR NONLINEAR HYSTERETIC MODEL (after Seaman & Whitman^)
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kt. This modulus is a function of mean stress and for a given stress represents the slope of the curve at that
stress level.
For loading
k^ ■ m ■ n A., a KLO)
and, for unloading and reloading
kt-% - n Aj/n a"-1/n (19) v
Note that in this model the modulus for unload-reload is larger than the modulus for virgin loading at any given stress level.
5.2.2 Triaxial Compression
A triaxial compression test normally consists of two phases. First, a hydrostatic confining stress, a , is applied to the specimen so that the principal stresses are all equal- to ac. Then, two principal stresses, 02 and a-, are kept constant at o while the third principal stress, a., is increased. For these conditions one of the components of the deviator stress is
ail " al " 1/3 (al + 2a3) " 2/3 <ara3> <20) If the material is Isotropie two principal strains, e^ and Ey are also equal, meaning that the corresponding component of deviator strain is
eil " el ' 1/3 (el + 2e3> - 2/3 <el " e3> (21>
Thus, for triaxial conditions the shear modulus may be determined from
21^- T^TT^ (22)
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Idealized behavior of a rock specimen loaded li> 21
triaxial compression as presented by Swanson '" Is shown
In Fig. 18. The relation between devlator stress and st/aln
Is linear up to yield. At stress states beyond yielding the
relation becomes nonlinear and plastic behavior occurs.
The modulus for unloading Is equal to that for virgin loading
to the yield point.
Volume change behavior Is the same as that for
hydrostatic loading at stress states below yield. At yield
the volume of the specimen begins to Increase even though
the mean stress Is compressIve and also Increasing. This
tendency for rock to expand when yielding Is termed dllatancy
and Is characteristic of almost all partlculate materials.
At low stress levels shear modulus Increases relatively
rapidly with mean stress; however, at higher stresses It
remains relatively constant. Torslonal wave velocities
were measured In cylinders of different granites exposed 2 2
to hydrostatic pressure between 1 kg/cm and 4,000 kg/cm
by Birch and Bancroft . From the wave velocities the modulus
of rigidity, which is identical to the shear modulus, was
determined and is shown as a function of mean stress in Fig. 19.
Also shown in Fig. 19 are values of shear moduli for specimens
of Charcoal Black granite and Cedar City tonalite determined
from triaxial tests performed during this study. The moduli
determined by Birch and Bancroft and those for the Charcoal
Black granite are in good agreement and increase approximately
with the 1/10 power of the mean stress. Values of shear
modulus for the Cedar City tonalite are, however, radically
different. At mean stress levels below about 5 ksl, the
shear modulus Increases with the 5/6 power of mean stress.
At higher stress levels, the shear modulus increases less
rapidly. One probable cause for this change in behavior
is the relatively high initial porosity of the tonalite.
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Fracture
De via tor Strain, ^j-fo
a) Shear Stress-Strain
r-ll
CO
CO CO 0)
t CO
c
Hydros tf
Dilatancy Curve
Volumetric Strain, ej^ + e2 + e
b) Volume Behavior
Flg- 18 ^Li5lNS^S-STRAIN BEHAVI0« OF ROCK,
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"^~" ■"^^
-
■ cn Q.
-
1 *. ^n f-4 ' OrH 1 r-l C
I X 0
c
ft
*c t^ TO
• 3
ii e 0
rt m 14 ^ f -d- JFi ^ X ^
i _i il \ i o 11 \ CM
u U \ •
r-l
i y* 11
'- 11 w '■" 11 V
| X) i j \ ! -3 41 \ _
- il \ - O 111-* \ V. > k —
•l—t i ^^^ v*^ ! r^ i ■ X ■ c 11 \ - i ^_ X. 0 ■ I V 1 u El X
i ^
-*- •H
a» 1 w 1
TO 1
O -
<—— OJ d) ^-1 o | u *J TO ^~
• -( ..-I 01 C •^ 1 r c •w 0 o 1 TO ^j •H H TO >-i ^ c i—i 1 -
| Ü o TO 4J
CO
>> 4-. c; •H r-i H rH U u TO
i VJ O >s 0 I oi a o M O ! J_I ^ c TO u 1
en u •H TJ TO I <U O 3 0) £ 1 — S OS O* O O i.
1
■
.1.
o
i i i
T -L. 1 i i i 1
o o
— o
_ o
o t
o
CO M M
CO
•r-l P2 CO H ^ M
^ M
e CO n Ö
1-1 #i D
w O cn 0) jgj ^ 4J CO
SSj
C g TO CO CU S b
o •^ o H H < H
^
«T»
bO
o
^^ « OT x TS>I <49 'sn^npow aeaqs
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Values of shear modulus shown in Fig. 19 are tangent
values, Gt, which refer to the t^lope of the deviator stress-
strain curve at a given stress vfclue. For nonlinear behavior
the tangent shear modulus is a function of mean stress and
may be calculated from
d(o, - a,)
°t - ^ j^h^r (23)
The functional relationship with mean stress may be written
as Gt- " c a (24) t m
in which c is a constant.
5.2.3 Uniaxial Strain
The uniaxial strain test is a special type of triaxial
test in which the lateral strains, 62 and e3, are equal to
zero throughout the test. One method of obtaining this
condition is through monitoring the lateral strains and
controlling the lateral stresses, Oj and o^, to maintain
zero strain. In soil mechanics, for the uniaxial strain
loading, the ratio between the lateral and axial stress is
called the coefficient of earth pressure at rest, K , where
K - !3 . (25) öl
Data from this test may be used to compute bulk and shear
moduli from the following equations:
öI G - 1/2 ^ (1 - K0), and (26)
k = 1/3 ^ (1 + 2K0). (27)
5.2.4 Poisson's Ratio and Young's Modulus
Two constants are necessary to describe the stress-
strain behavior of an Isotropie elastic material. One set
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of constants, k and G, which separate volumetric and
deviatoric behavior have been described previously.
Another pair of constants which are commonly used are
Foisson's ratio, v, and Young's modulus, E. The constants
E and v are derived directly from a triaxial test in which
the lateral stresses, 02 and o^, are equal to zero. For
this special test condition.
E - i, and (28) E 1
- - -* (29)
For more general test conditions
9kG E - 3k + G , and (30)
The use of tangent values of bulk and shear moduli, kt and
Gt, in equations (30) and (31) will result in tangent values
for Foisson's ratio, vt, and Young's modulus, Et.
For hydrostatic loading the deviatoric stresses and
strains are zero and G is undetermined. Therefore, E and v
are also indeterminate from a hydros tat. For a triaxial
test with a3 equal to zero, E and v may be computed from
equations (28) and (29). For a triaxial test with a~ unequal to zero but constant, tangent values of E and v may be computed from
(32)
(33)
Et - da^
, and
vt ■ •
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For more general conditions equations (30) and (31) must be used.
For unlaxlal strain tests the following expressions oay be used _
E-^ —n-hg—-•"'* w
v- r-^g- . (35)
5.2.5 Yield and Fracture Criteria
In principal stress space the restraint a2 m a3 defines a plane which Includes the a,-axis and the axis of the yield surface shown In Fig. 14. As a« - a3 Is a condition maintained during the trlaxlal test all stress states In this test lie In the c^ - a« plane. Thus, yield and fracture criteria may be described by a curve In this plane. Curves representative of different failure criteria are shown In Fig. 20 with J^ plotted vs. V J* on orthogonal axes. The stress path for a constant o3 trlaxlal test Is also shown In Fig. 13.
A thorough discussion of yield and fracture surfaces as they apply to the behavior of rock has been given by Swanson . The yield surface defines all stress states at which the rock ceases to be an elastic material. At stress states within the yield surface some form of elasclc equations govern the material behavior. At states on the yield surface equations from plasticity govern the behavior. It has been shown that most rocks exhibit strain-hardening behavior; I.e., the Increase of stress beyond Initial yield causes the yield surface to move outward. Continued Increase of stress causing outward movement of the yield surface will eventually result In failure of the rock. The locus of all jtress states causing failure Is called the fracture
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Pi I 3
o CM
00 •rl
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Wm/M'mmm
surface or failure surface. <
5.3. Analysis of Ekperltnental Results
Experimental results are presented In a form
consistent with the elastic-plastic constitutive model
presented earlier. Elastic properties are presented as
functions of mean stress and are given In terms of tarigent
values which are compatible with a nonlinear incremental
form of elasticity equations. Yield and fracture criteria
are presented in the form J« " (Ji)•
5.3.1 Charcoal Black Granite
Typical volume change data from a constant confining
pressure triajcial test is shown in Fig. 21 along with a curve
representing the nonlinear hy^teretic model fitted to the ■■ experimental data. The constants for the model were conven-
lently determined from logarithmic,plots of the data, In
the middle portion of the curves experimental results and
the model are in close agreement. At relatively low stress
levels, less than 2 ksi, the model predicts, stresses that
are smaller than those measured. Fracture of this specimen
occurred at a mean stress of 17 ksi and yielding had begun
at about 14 ksi which results in dilatant behavior of the
specimen at thesö stress levels. T^ius, as would be expected
the model and experimental results dp differ at stress levels
greater than 14 ksi for this particular specimen.
Tangent values of bulk modulus, Kt, were determined
from the experimental data and plotted as a function of
mean stress in Figs. 22 and 23. These values represent
the computed slope between actual consecutive data points
rather than the slope of a smooth curve drawn through the
data points. This procedure Introduces "noise" i,n the
plots since the data points are rather close together and
the Uncertainity in the computed volumetric strain is rather
large in comparison with the change in volumetric strain over IIT RESEARCH INSTITUTE
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. ...._ ,- ■ . - ■■ . ■ ■ ::•. :.•,.• ■■ ■■ . ■■ •■■■v BMHWiaiK^fWffaMlgByW^Ba^^ 11
18
16
14
12
10
0 n o 3
to (0 0)
co 6 c CO 0) as
Test No. 12 2 in.-dia. Specimen o.j ■ 5 ksi
Model (Load)
Aj^ - 2.1 x 10^ ksi
Model (Unload-Reloac)
v 'vi
2.6 x 105 ksi
e - 2.5 x 10"4 ve
i I 8 12 16 20 24 28
3.3 -4 Volumetric Strain, ev, in /in"' x 10
Fig. 21 MEAN STRESS VS. VOLUMETRIC STRAIN, CHARCOAL BLACK GRANITE
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^Sj*w?PW8»W5«(l^ WiWgSwW«*^^
M
i
l-l 3
14 — —
14 o
0 Te8t. i2 2-in. dla. granite
12 - 6
D
Test 14 oo
Test 34 ^ 4 A 10
8 -
o c
oooo0o «^ n DDDDa
6 -
4
m ̂ 1 ■ A
2 Solid Symbols indicate Hydrostatic Data
_J 1 J i I l l i i i
8 10 12 14 16 18
Mean Stress, <J , ksi tn'
20 22
14 U
1'-
10
8
6
4
2
° -
4-in. dia. granite 0
oo o ^
_ 0 Test 9 o
A Test 11 0
- O Test 19
■ ■ <<
4
A ^
'*? O
Y Solid Symbols indicate Hydrostatic Data {
1 1 -J L L -J 1 ' i L.- 1 1 8 10 12 14 16 18 20 22
Mean Stress, a , ksi
Fig. 22 BULK MODULUS VS. MEAN STRESS - 2" 0 AND 4" 0 CBG
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: ., . .. ,. ■ -■ ., ;
CO M
•> 4-1
^5
CO 3
i-i 3
•V
3 CO
•I-I CO
(O
3
3 PQ
12 p-
10 -
16
14
12
10
8
6
4
2
Test 20 o 10 ksi
" 16 A 5 ksi
12-in. dia granite
o
o
Solid Symbols Indicate Hydrostatic Data. , , i
10 12 14 16 18 20
Mean Stress, orm, ksi
0 o
[— m
4
Test 28
" 27
o 5 ksi
^ 5 ksi
t 4 ■
■ D " 29 DD n"D 30
A 10 ksi
□ 10 ksi
A > S ^ a Q 0 r '% ■ 32-in. dia granite
r / ■ t D
L/ t r * •
■ &
Solid Symbols Indicate static Data
Hydro-
1 M. _L w^m —_ J I l 1 1 L I 10 12 14 16 18 20
Mean Stress, o . ksi m
Fig. 23 BULK MODULUS VS. MEAN STRESS - 12" 0 AND 32l, 0 CBG
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Wmsmmmmmmmmmmmm ■■v-■7^.ri;v,;1^>^-i■^..^v-,;.«:.i^;v^t■■^■:r^^'^^■■^:v;>■ ■,';■.■■ ■■..-■■; .- -,;-: ......^-,..:■ . ....
the short interval between data points. Each plot Is
superimposed on the values of bulk modulus predicted by
the nonlinear hysteretlc model for the particular core
size. Several trends are Immediately apparent. First,
the experimental data fits the model best In the hydrostatic
range of each test, and departs from the model at low
stress levels and at high stress levels where yielding la
to be expected. Second, the fit to the model Is best for
the small specimens and worse for the large specimens.
This Is probably a result of the relatively early slippage
that took place In the larger specimens. The larger specimens
began slippage at low levels of devlator stress, so that
earlier departure from the model Is to be expected. Of course.
It Is to be remembered that the model was developed for small
rock specimens.
Table 2 Is a summary of the model parameters for the
tests on Charcoal Black granite. The smaller cores behaved
quite consistently, and the model parameters were simply
averaged to produce the final parameters for each test.
The larger tests were less consistent, particularly with
respect to the values for A^. The final parameters for the
32-ln. specimens were obtained from a composite log-log
plot of data for tests 27, 28 and 30.
An Interesting comparison may be made between the
analysis of an ideal packing of elastic spheres as discussed
earlier and the observed hydrostatic behavior of the rock
specimens. Values of "nM in the nonlinear hysteretlc model
vary from 1.59 to 1.93 with an average of 1.74 for the
specimens of Charcoal Black granite. The corresponding
values of "n" for the ideal packing is 1.5. For granular
soils n values between 1.5 and 2.0 have been observed^.
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:- gsfp^enw ■■■ "■.-.
^> CO H
O
CO
öl H H
- o N X
•r4 4-1 (/)
C U) CO VJ (U o So c
o
OH io CO
(0 0) H
i (0
<N m o a»
oo
CO
oo m <t vO o t-t ON vt" m T-i CTN n 00 ^t O 00
• • • • eg <N
• • • o
• • <N
• • • O O O i-l rH O
I-H CNJ cn vo »n vo
vO O i-l 00 f^» 00 00 <T> vO !T> o r*
m in m o m oo o oo
mom mom
«N -d- -d- rH r-l CO
ON r-l a»
CN
m m o
vo r«. o rH «^1 cs'
r-l vt rH
m m o o
r^ oo ON o (N OJ <N «^
fvi <N CM CO
3
]
i
I I i I I
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^^^f^lPI^^SS^ T#^■*■■■^^*«Wli.^fS9«WW*^«?:-■"w^■■■':■!^,:■ ■■ ■ .- -■
Typical devlatorlc stress and strain data from a
constant confining pressure trlaxlal test, a_ « 5 ksl,
are shown In Fig. 24. The curves are very nearly linear
at stresses less than approximately 30 ksl which Is the
level at which Initial yielding of the specimen occurs.
Also the unload curve Is nearly elastic with a very small
residual strain. Similar data was obtained from tests at
other confining pressures except the unconflned compression
test, cu ■ 0. For this test the slope of the devlatorlc
stress vs. devlatorlc strain curve Increased slightly an the
stress Increased meaning that the shear modulus, G, also
Increases with stress at low stress levels.
Tangent values of shear modulus, Gt, were determined
from the experimental data and are shown in Fig. 24 (b),
25 (b), 26 (b) and 27 (b) for specimen diameters of 2 in.,
4 in., 12 in. and 32 in. respectively. The stress paths
of the particular tests considered for each diameter are
shown in Figs. 25 (a), 26 (a), 27 (a), and 28 (a). As
observed from the data the shear modulus increases with mean
stress especially at the low stress levels. An equation
of the form
Gt - ca/'lO, (36)
in which "c" is a constant, was fitted to the experimental
results and is shown in Fig. 25 through 28. As relatively
little inelastic behavior was observed in the shear
deformations the model for shear modulus is the same for
both loading and unload-reload. Model predictions are in
agreement with observed behavior except at low stresses.
A summary of the mathematical models for bulk
and shear moduli along with the constants determined from
the experimental results is presented In Table 3. Values
of Young's modulus were computed from equation (30) using
the predicted values of bulk and shear modulus and are shown
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■ ■• ■■■■■w.■■.,;. i
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■ :■ - ■■ :■■■:.■, ■ ■ -,;■:.■ . . ■■
•rl CO
40
36
32
28
24
CO o I
CO CO 0) u
CO
o 4J CO •rl > 0) Q
20
16 -
12
8
Test No. 12 2 in. diameter
5 ksi Fracture
8 16 29 32 40 48
Deviator Strain, Cj^Eß, in/in x 10 -4 56
Fig. 24 DEVIATOR STRESS VS. STRAIN, CHARCOAL BLACK GRANITE
54
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Wt^lSim^r^mm^,-^-.,-^ -■■■■■■'■■-■ :'■■:■■■-
Mean Stress, a,., ksi
a) Stress Path
16
12 on o
1 8
.3 | 4
Model (Unload-Reload) — ——-r--^-^^- Model ^^ 14 (Load)
Young's Modulus 12
1-1 14 Model
Mean Stress, a , ksi
b) Shear Modulus and Young's Modulus
Fig. 25 TANGENT MODULI FOR CHARCOAL BLACK GRANITE, 2-IN. DIA.
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imufc'vvmm i nsManwsMn »^^iRe^wHMfrff^imsfi -. Wyf'j^f^armn^Krmfi^'K^'.rrrr^rt
32
24
16 •■-I
J2
.CM g
fe
Test 11
24 28
Mean Stress, a , ksi
a) Stress Path
16
12
CO o
x 8
J2
§ 4 3 3
/
r ^-^Model (Load) Model (Unload-Reload)
^ ET
19
11
■^ "Model 19
J L 8 12 16 SO
Mean Stress, a , ksi in
J L 24 28
b) Shear Modulus and Young's Modulus
Fig. 26 TANGENT MODULI FOR CHARCOAL BLACK GRANITE, 4-IN. DIA.
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ISS' BW^S^S.WÄÄWfMlBRa^ vS3«^«ES«BS,MM!»l(¥^P^-w^if«^^!1-i-:^.vp^^^
32
24
16
J2
^
8
Test 16, 21
Test 20
0 4 8 12 16 20
Mean Stress, a) Stress Path
Mean Stress, a , ksl m
24 28
O
03 3 3
Mean Stress, a , ksi m
b) Shear Modulus and Tangent Modulus
Fig. 27 TANGENT MODULI FOR CHARCOAL BLACK GRANITE, 12-IN. DIA.
57
^.■V;^: ■■:,. ^r.^^.i-^.^iu-;,.^;.,,,;
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•"irrrnwrnrrowiimriiM^ imiinMniiPiiinii n.. uniii
24
16
5 8
4 8 12 Mean Stress
en o
•rl
CO
(0 3 3
16 — 28
12 ^/'"'
— — ■%
30
8 —
^ u 4
'Gt
1 1 1 l 1 4 8 12 16 18
Mean Stress a , ksi
Flg. 28 TANGENT MODULI FOR CHARCOAL BLACK GRANITE, 32-IN. DIA.
58
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,,,,, MWRmmnrwr >
Table 3
ELASTIC PROPERTIES OF CHARCOAL BLACK GRANITE
Bulk Modulus
loading, kt - nAj1^ a. ^ m n
unload - reload, kt - nAg <?„,
Shear Modulus 1/10 loading, Gt - C ö^
unload - reload, G - C o
. G^ and 0m in ksi
1/10 , G^. and ai in ksi
Young's Modulus
9 \ Gt
Poisson's Ratio
V. 3 kt • 2Gt
Specimen Diameter in inches n
Al in ksi
A2 in ksi C
2 1.59 1.72 x 105 1.72 x 105 3,900
4 1.89 9.05 x 105 10.7 x 105 4,800 12 1.93 5.34 x 105 13.5 x 105 4,100
32 1.56 2.37 x 105
59
mmmrm»*
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-■ i <m&mmmm
as a function of mean stress in Fig. 25 through 28. Poisson's
ratio values were computed from equation (31) and are shown
in Figs. 29, 30, and 31 for the different specimen diameters.
Again, except at stresses below 1 ksi the model fits the exper-
imental data.
5.3.2 Cedar City Tonalite
The nonlinear hysteretic model was fitted to the
various core sizes of Cedar City tonalite by use of log-log
plots of mean stress versus volumetric strain. The resulting
model parameters were used to compute bulk moduli in the
same fashion as was done for the Charcoal Black granite.
Figures 32, 33 and 34 show the actual bulk moduli as a
function of mean stress. The solid symbols indicate data
from the hydrostatic portions of the various tests, the open
symbols the triaxial compression portions. In general, the
hydrostatic data fall near the model and the triaxial data
depart from the model. The data points do not scatter
symmetrically about the model because the model was fit
to the volumetric strains rather than the bulk moduli.
The same observations apply to this data as to the
corresponding Charcoal Black granite data. The model for
each core size fits best in the intermediate stress ranges,
and the data scatter increases with specimen size. The
nonuniformity of this rock type is particularly noticeable
in the 12-ln. cores. Tests 17 and 38 had quite different
moduli below 5 ksi, but appeared to converge to the same
stiffness above 7 ksi. This may be expected if the existing
cracks are closing in this pressure range.
The scale effect is shown in Figs. 35 and 36. Figure
35 is a plot of the mean stress versus volumetric strain
predicted by the model for the three specimen sizes. Figure 36
is a common plot of the bulk moduli. The major difference between
the 2-in. and 4-in. models is that the 4 in. model is slightly
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0.5 I—
o l! 0.4 5 ? 0.3 c o CO
.2 0.2 ,2
o.i
0 Test 12 A Test 14
O Test 34 2" CBG
^r V ZModel
0 10 20 30
Mean Stress (ksi)
40 50
0.5
.2 0.4
« 0.3 "c
1 0-2 •i-i
o.i
o D
Test 9
Test 11
Test 19
o o
Model
4" CBG
10 20 30
Mean Stress (ksi)
40
Fig. 29 POISSON'S RATIO VS. MEAN STRESS FOR 2 IN. 0 AND 4" CHARCOAL BLACK GRANITE
61
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mmmmm wmmfmmmmmmmmmmmmmmm •""»(««»«««»««»««SBW^^^äW^i»«^
.5
.4
.3
.2
.1
A
A Oeo^
D CP
0 Test 16
A Test 20
D Test 21
12" CBG
Model
10 20 30
Mean Stress (ksi)
40
Fig. 30 POISSON'S RATIO VS. MEAN STRESS FOR 12" (3 CHARCOAL BLACK GRANITE
.5 0 Test 29-30
.4
.3
AA A Test 27-28
.2 4 y* -^
.1
| |
0 10 20 30
Mean Stress (ksi)
40
Fig. 31 POISSON'S RATIO VS. MEAN STRESS FOR 32" 0 CHARCOAL BLACK GRANITE
62
1 --■ niiTMlftMWIIWMiMMWrtlWMr.lLHUUIJ I...
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O
CO X
CO 3
i-i
3
r-l
3 03
2-in dia. tonallte
25 26
O " 33 SHADED SYMBOLS INDICATE HYDROSTATIC. STRESS .STATE
x 10 = 5 ksi
5 10 "
15 "
8 10 12 14 16 It? 20 22 24 26 28 30
Mean Stress, J^ ksi
Fig. 32 BULK MODULUS FOR 2" CEDAR CITY TONALITE
o
■r-l [0
CO 3
3
7
6
5 -
4 _
3
2
4-in. dia. tonalite SHADED SYMBOLS INDICATE HYDROSTATIC STRESS STATE
- D O
- ^ A ^7 fn = 1 .37
— D
D c ▲ A^^f/iAi= 1.77 x lO"1
— V
G0 V z ▼ v S^b / «Test 36 5 ksi
35 5 "
1 mo&k ̂ ^T^ A ^ ^ 18 10 "
J 1 ,
^ o o
1 1 1 i -L 1 1 1 1 1
22 15 "
23 15 "
1 1 2 4 6 8 10 12 14 16 18 20 22 24
Mean Stress,o„,. ksi tn'
Fig. 33 BULK MODULUS FOR 4M CEDAR CITY TONALITE
63
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*,ie.m!mm*mm,™mrmm^
CO o 1-1
•o
pa
6
4
3
2
X 3 H
CO
(0 3
O Test 17 5 ksi
O Test 33 10 ksi
b = 1.32
2-in. dia. tonallte o
SHADED SYMBOLS INDICATE HYDROSTATIC STRESS STATS
= 2.08
10 11
Mean Stress, (?„,, ksi
FIG. 34 VARIATION OF BULK MODULUS FOR CEDAR CITY T0NAL1TE, 2-in, 4-in. and 12-in. DIAMETER
22 — A"
20 —
18 — 24" /
16 — /
| 14 __
B12 —
CO
g io U 4J w 8
c v 6
2u
—
//
/ 12"
V 4 — y /
2 — y^^
1 1 1 .002 .004 .006
Volumetric Strain
.008 .010
Fig. 35 VOLUMETRIC STRAIN FOR CEDAR CITY TONALITfi MODELS
64
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o
f-i CO
3
3 CO
5 Immm
4 __
3 — _-— —'2
2 ^^ ̂ ^ - 12
1 €^ -^
V\ 1 1 i 1 1 L 1 1 0 6 8 10 12 14 16 18 20
Mean Stress (ksi)
Fig. 36 BULK MODULUS FOR CEDAR CITY TONALITE MODELS
65
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»Llfler below 3 ksl. This results in a horzontal displscement
of the curves in Fig. 35. If Fig. 35 were extended to higher
stress levels, the 2-in. and 4-in. curves would cross as a
result of the higher 2-in. bulk modulus. The actual differences
in these curves are probably a result of specimen variation
rather than scale effects. The 12-in. specimens appear to be
significantly less stiff than the smaller specimens.
Figure 37 shows the scale effect upon shear modulus
G and elastic modulus Et. Data from all tests are included,
and again the scatter is caused by the short interval between
data points. It can be seen that the 2-in. and 4-in. specimens
were not significantly different, and that the 12-in. specimens
were less stiff at lower mean stress values. The shear modulus
did not fit the one-tenth power of mean stress model, so fair
lines were passed through the data by eye. The elastic
modulus model was computed using values of the bulk modulus
models in Figs. 32, 33 and 34, and appears to represent
the experimental elastic moduli well.
Figure 38 shows plots at Poisson's ratio for the
various size specimens. The typical behavior is to start
out somewhat below the model and rapidly increase to a
value greater than would be predicted by this model. The
tests having 15 ksi confining pressure maintain a value
of approximately 125% of the model value for a period before
yielding begins, while the tests at lower confining pressures
appear to maintain a monotonic increase. As the yield point
approaches, the value of Poisson's ratio may increase because
of the dilatancy of the specimen.
5.3.3 Uniaxial Strain Tests
Uniaxial strain tests were conducted on two specimens,
a 22-in. dia. Cedar City tonal!te specimen and a 32-in. dia.
Charcoal Black granite specimen. The results from this type
of test should be applicable to unidirectional compression
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t^m^mr^m---.:-^-'-■:--:^-->^;/^^'^^^^M^^-^^'i ■■■• i. . ■ ■.:'i*-iI-1».»|,".-»-«fr,-p..tf.- ■:-.r.VI^i.l. ■■..■ .
C=r = r= z z z
< " HCVICMCM^r«*»* stCM CM Q r-i r-t
H W W H
< O > • ^ ► + K
o m
•X) CM
w vO 1^1 <N ä <t § CM H
CM S CM •H H
(0 O M
O §t ^ B
o 3 OC o ^-1 n
«5 Oi (0 o
X) dJ (K <-* ^ 4-1 l-l to ->
>* D f-l C O
CO Q Ä s
CM
00
vO
CM
S O
en
00 •i-i
vC IT) m CM
.01 x jBy[ «'o JO ^a 'TTnP0W
67
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■ mmmmmmmmmmmmmmmm ■■iiwiwumMiMiiii mmmmmmmmmmmmimmm
5 \-
(0
1 D 25 • ■ 5 ksi
| 0 26 • • 10 ksi L A 33 - • 15 ksi
3 h-
2" 0 CCT AA
c o w
2(3kt - G,.)
I I I I 6 8 10 12 14 16 18 20 22 24 26 28 30
Mean Stress (ksi)
.5h- D 35 - 5 ksi O 36 - 5 ksi N7 22-15 ksi
15 ksi
4" 0 CCT
O 4J to
.4 _ A 23 - ]
co .3 — 'c o
(0 .2 — (0 •H O 0, .1
1 |D
° o
OocPD 0
-B
V 2^
s^^7
^
I I I I J i i I I 6 8 10 12 14 16 18 20 22 24
Mean Stress (ksi)
u . co .4 06
.M.3 B O co 9
•I-I
S.l
A 17
O 38
5 ksi
10 ksi 12" 0 CCT
I I I 2 4 6 8 10 12 14 16 18 20
Mean Stress (ksi)
Fig. 38 POISSON'S RATIO FOR CEDAR CITY TONALITE
68
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■MmmmMMmntaffi .m^M^ummmmmw^'r^'--,-^. ■■ ■--■■■■■..■..■■...■.■v'
of an element in a rigidly confined mass or plane-wave
propagation. The radial strains were monitored during the
test by the auxiliary averaging strain gages described
in the experimental apparatus section of this report.
Confining pressure was controlled to maintain these gage
readings as near zero as possible.
Figure 39 shows the axial and lateral strains and
the stress trajectories for both tests. As can be seen,
the radial strains did go tensile by about 250 micros trains
in test 31 and 100 micros trains in test 32. The Cedar City
tonalite (test 32) failed at an axial stress of 20 ksi.
The behavior of the Charcoal Black granite was
somewhat more complex, primarily because this specimen was
able to support load after slippage, and the test was
continued for two full cycles. The offset on the unload
cycle at 11,5 ksi was caused by a gage failure. The offset
on the reload cycle at 26.5 ksi was accompanied by a major
rock shift.
Figures 40 and 41 show the shear strain and volumetric
strain for both tests. Note that for this test condition
there appears to be little difference between the two rock ft ft
types. Both have shear moduli G between 4 x 10 and 5 x 10 ,
Any curvature in the Charcoal Black granite shear modulus
is swallowed by the initial zero offset, which may or may
not be real. The bulk modulus for the Cedar City tonalite 6 fi
increases from 1.6 x 10 to 5.2 x 10 ksi as mean stress
goes from zero to 9 ksi. The Charcoal Black granite bulk fi ft '
modulus ranged from 1.7 x 10 ksi at 1,5 ksi to 4 x 10 ksi
at a mean stress of 10 ksi. Corresponding values for elastic
modulus and Poisson's ratio are listed below:
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I
) '■
I
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■"■'••■■■"•■■
Test 31 CBG
0 4 6 8 10 12 14 16
Mean Stress (ksi)
Lateral Strain .001 .002
Axial Strain 003 .004
Fig. 39 UNIAXIAL STRAIN TEST
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wraww^"-?-*^«^^^^^
30 i—
03 (0 01 U 4J w M O 4J (0
•■-< > <u a
20
10 —
16
.002 .003 Shear Strain
Fig. 40 SHEAR BEHAVIOR FOR UNIAXIAL STRAIN TESTS
•i-i
to
CO (0 <u u u M
0)
1^
12
10
8
Test 32 CCT
.002
T" .002
Unload Cycle Two
1 1 .004 .006 .008
Volumetric Strain
Fig. 41 VOLUMETRIC STRAIN FOR UMIAXIAL TEST
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—"" TnTT^'in'TI'ITrTirTriMliHIMM
Charcoal Black Granite Cedar City Tonalite
% G K E V G k • E V
2 4 2.9 8.3 1 .03 4.5 3.5 9.5 .05
4 3.3 j 8.5 .07 4.4 10 .12
6 3.8 8.9 .11 j 7.0 11 .24
8 4.2 9.1 .14 10.5 12 .31
5.4 Strength Properties
Figure 42 indicates the maximum stress levels attained
by each specimen. Due to a less favorable intensification ratio
in dhe 14-in. triaxial eel?, there were no failures of the 12-in.
specimens. Future programs would need to employ higher stress
levels to insure failure.
The 32-in, dia. Charcoal Black granite specimens reached
maximum stress levels of about one half that of the 2-in. specimens
The actual scale effect is probably somewhat greater. Slippage
along a joint plane will produce instant failure in a 2-in,
specimen, while a 32-in. specimen not only survives minor slippage,
but can be loaded to greater stress levels.
The Cedar City tonalite was much more variable. As
might be expected from a weathered rock, the strength at low
mean stress levels is quite low. This corresponds to a low "c"
value on a plot of the Mohr-Coulomb failure envelope.
Enough data was not obtained in this program to apply
any statistical theories, such as those of Weibull or 15
Grobbelaar . It is hoped this will become possible when more
data is accumulated.
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• ■■■..■■ ■ ■ ■ :■■.-■■ ■.■■.
30
J? 20-
? 10 —
Charcoal Black Granite
0 Solid Symbols Indicate Failure
#
D
— J Symbol
O Dia. 2"
0 / ♦ D D 4"
* A
1
A
i o 12"
32" o 1 1
0 10 20 30
Mean Stress (ksi)
J
30 _ Cedar City Tonalite
Solid Symbols Failure
Indicate 0
20 ■
• D Symbol
O Dia. 2"
10
■ D D
A
4"
12"
Qh V 1 1
O 24"
1 10 20 30
Mean Stress (ksi)
40
Fig. 42 MAXIMUM VALUE OF Vj]" REACHED FOR ALL TESTS
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wmwhmtmw&zmfymmmmmimM wmatm/K *Mmmm
I
I
6. SUMMARY AND CONCLUSIONS *
Over the course of this program, 27 trlaxlal tests | were run on samples ranging from 2 In, to 32 In. dla. This Is the first time that specimens of this size have ever been tested under laboratory conditions. Because of the large volume of data collected, the results of this program _ are presented In term of a nonlinear hysteretlc model proposed J by Seaman and Whitman^ and having the form
] "in " Vv loa<lln8
"m " A2(ev"evpn unloadln8 1
. ..„.. ]
i i i I
a_ Is mean stress m e Is volumetric strain
e , Is residual volumetric strain.
The data fit this model well at Intermediate stresses. However, the model predicts that bulk modulus Is zero when mean stress equals zero, and bulk modulus goes to Infinity at Infinite mean stress. In fact, rocks display a finite bulk modulus at zero mean stress and a constant bulk modulus under high stresses. In spite of this, the data depart from the model only below stresses of about 3 ksl and f at higher stresses when yielding occurs.
I The model parameters as fitted to each core size are summarized In Tables 4 and 5. Up to 12-in. dla. it seems the Influence of specimen size on the mechanical ¥ properties is small. There is not enough data on the larger samples to draw definite conclusions. The largest scale 'M effect was found in the Cedar City tonallte at mean stress levels below 5 ksl. Both the model and the experimental data indicated low bulk modulus and elastic modulus in this
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MKMHlMIMBmmWWMßHWM^^ -'l:'.;.'.■': ^V'1 1:"'
range, although these parameters increase rapidly with mean
stress.
The Influence of specimen size on strength Is
pronounced on both rock types. The 32-In. Charcoal Black
granite specimens failed at stress levels about one half
those of the 2-in. specimens. The mode of failure also
was markedly different. The 2-ln. specimens failed
catastrophically, while the 32-in, specimens failed initially
by a series of small slips.
With the accumulation of more test data it may
become possible to develop a model which more clearly
predicts the behavior of the large rock cores. It may
also become meaningful to verify statistical hypotheses.
It should be noted that with the larger cores, the
rock depicted a load carrying capacity even after failure
had initiated. This is often observed in the field. Besides,
the mechanism of failure was different in these larger
cores. This is Significant in that at about 30-in. die.
or larger perhaps the type of rock failure obtained appears
to be similar to that observed in the field. Perhaps models
developed for this size can predict results closer to field
observe tiooa.
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^»vsmmmmmmmmimmmm
0)
Xi
I vO SO rs cn o CM <M O o en H m CM f-l CM Os < <-! CM H i-4 r* CM O SO
« • * « • • • U • o o i-l H o CM CO O
00 e
00 en «* so ON d) i-4 <* o 1-1 ON «* m H ON CM s 00 *• O oo
HvO M i-l i-4 CM CM CM i-l o •H cn CM OS SO < o j « • • • • • • • u • • • • I
H O o i-l i-4 O i-l 0) o O i-4 H j X 0.
(0
•o 0)
e i-J CM cn SO O i-4 00 en •o oo en m m 0
C SO in so 00 OS sO o> o s r^ m oo o 00 • • »
i-l H • 1
i-l H •
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CM 0
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0 m s » m o m m m m O m m o o , cn •J iH H i-l r-4 «-» lu
S V (tf 1
1 w (0 cs <* .* OS fH OS sO r** f-i O 1^. 00 OS O i-4
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: ■ ,; ; .■...■ ■. ■■ ■ . ■ . . ■
m 0)
i-4
5
m 1 o
m a» CO m 00 iO CM CM
i-4 • • • SO H
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m o to m so CM i »"", vD vo i-4 m m m co CM SO
m O 00 ON oo r» o 00 ** 1^ O X o m <*i H H *• f4 O co '-4 i-4
<
00 ** o co ts. co m St •D CM 00 \ i ö CM vO vO <f CM CM CO vO co CO O
r-4 H H H H i-4 H 1-1 i-4 r-l CM
i ^ o m mom m m o m m m O i ^ H H i-4 t-4 r-l H Iw
4J w ^d- m vo co m so oo CM CO r^ oo CM 0) <M CM CM CO CO CO 1-« CM CM i-4 CO CO H
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inWfTO^tJTOwwtwff^^wiH^
REFERENCES
1. Rapid Excavation, National Academy of Sciences, Wash. D.C.,
Publ. 1690, 1968, 48p.
2. Proc. Advisory Conference on Tunneling, Rept. on Tunneling.
1960-1980, Organization for Economic Cooperation and
Development, Washington, D.C. June 2?-26, 1970, 26p,
Appendices and Comments.
3. Standard Method of Test for Triaxial Compressive Strength
of Undrained Rock Core Specimens Without Pore Pressure
Measurements, ASTM Test Designation D2664-67.
4. Standard Method of Test for Direct Tensile Strength of
Rock Core Specimens, ASTM Test Designation D2936-71.
5. Standard Method of Test for Unconfined Compressive Strength
of Rock Core Specimens, ASTM Designation D2938-71.
6. Standard Method of Test for Deformation Moduli of Rock
Core Specimens in Compression, ASTM Test (In Preparation).
7. Rice, G. S. and Enzian, C, Tests of Strength of Roof
Supports Used in Anthracite Mines of Pennsylvania,
U. S. Bureau of Mines Bull. n303, 1929, 44p.
8. Greenwald, H. P., Howath, H. C, and Hartmann, Experiments
on the Strength of Small Pillars of Coal in the Pitts-
burgh Bed, U. S. Bureau of Mines Tech. Paper n605,
193?, 22p.
9. Burton, L. D. and Phillips, J. W., Communication to
Evans and Pomeroy (11).
10. Mlllard, D. J., Newman, P. C. and Phillips, J. W.,
The Apparent Strength of Extensively Cracked Materials,
Proc. Phvs. Soc. (London). v68, ser B, 1955, p. 723-728.
11. Evans, I. and Pomeroy, C. D., The Strength of Cubes of
Coal in Uniaxial Compression, Mechanical Properties
of Non-Metallic Brittle Materials, ed. W. H. Walton, III IISEARCH INSTITUYI
78
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<ff^<mmmii^mi»mm-' ■ . ,.<M-,———————
Interscience Publishers, New York, N.Y., 1958,
p. 5-28.
12. Holland, C. T., The Strength of Coal in Mine Pillars,
Proc. Sixth Symp. on Rock Mech.. U. of Missouri at
Rolla, Rolla, Mo., 1964, p. 450-466.
13. Weibull, W., A Statistical Theory of Strength of Materials,
Ineretensk Akad. Handl.. nl51, 1939, p. 5-45.
14. Protodyakonov, M. M., Methods for Evaluating of Cracks
and Strength of Rocks in Depth, Fourth Intl. Conf.
Rock Mech. and Strata Control. Columbia U., New York,
N.Y., 1964, Addendum.
15. Grobbelaar, C, A Theory for the Strength of Pillars.
Pillarco, Pretoria, S. Africa, June 1970, 103p.
16. Epstein, B., Statistical Aspects of Fracture Problems,
Jour. APPI. Phvs. v 19, n2, Feb. 1948, p. 140-147.
17. Bieniawski, Z. T., Mechanism of Brittle Fracture of
Rock, D.Sc (Eng.) Thesis, U. of Pretoria, S. Africa,
1968.
18. Glücklich, J., Cohen, L. J., Size as a Factor in the
Brittie-Duetile Transition of Some Materials,
Int. Jour, of Fract. Mech. v 3, n4, Dec. 1967, p. 278-289.
19. Glucklich, J., Cohen, L. J., Strain-Energy and Size
Effects in a Brittle Material, ASTM Materials
Research and Standards, v 8, nlO, Oct. 1968, p. 17-22.
20. Baecher, G. B., The Size Effect in Brittle Fracture,
M. S. Thesis, Mass. Inst. Tech. June 1970, 190p.
21. Swanson, S. R., Development of Constitutive Equations
for Rocks, Ph.D. Thesis, Univ. of Utah, Dec. 1969, 140p.
22. Adams, F. D. and Nicholson, J. T., An Experimental
Investigation into the Flow of Marble, Phil. Trans.
Roy. Soc. (London). Ser. A, v 196, 1901, p. 363-401.
IIT RESEARCH INSTITUTE
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23. von Karnwm, T., Festigkeitversuche unter Allseitigem Druck, Zeitschr. des Vereins deut. Ing.. v 60, 1911, p. 1749- 1757.
24. Griggs, D. T., Deformation of Rocks Under High Confining Pressures, J. Geol.. v. 44, 1936, p. 541-577.
25. Griggs, D. T., and Miller, W. B., Deformation of Yule Marble: Part I—Compression and Extension Experiments on Dry Yule Marble at 10,000 Atmospheres Confining Pressure, Room Temperature, Geol. Soc. Am. Bui., v. 62, 1951 p. 853-862.
26. Handln, J. W. and Griggs, D., Deformation of Yule Marble: Part II—Predicted Fabric Changes, Geol. Soc. Am. v. 62, 1951, p. 863-886.
27. Griggs, D. and Handln, J., Rock Deformation. Geol. Soc. Am.. Mem. 79, March 1, 1970, 382p.
.28. Baidyuk, B. V., Mechanical Properties of Rocks at High Temperatures and Pressures. Consultants Bureau, Plenum Pub. Corp. New York, 1967.
29. Morgenstern, N. R. and Tamuly Fhukan, A. L., Non-linear Stress-Strain Relations for a Homogeneous Sandstone, Intl. Jour. Rock Mach. Mng. Sei., v. 6, 1969, p. 127-142.
30. LaMori, P. N., Static Determination of the Equation of State of Cedar City Tonalite, DASA Rent. No. 01-69-C 0053, May 1970, 78p.
31. McClintock, F. A., Walsh, J. B., Friction on Griffith Cracks in Rock under Pressure, Proc. 4th Nat. Cong. Appl. Mech., Berkeley, 1962, p. 1015-1022.
32. Brace, W. F., Brittle Fracture of Rocks. Proc. Intl. Conf. on State of Stress in the Earth's Crust. American Elsevier Publ. Co., New York, 1964, p. 111-174.
IIT RESEAICH INSTITUTE
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WMBBIiyiMIIIJIIIIIWIM ' '
i
33. Murrell, S. A. F., The Effect of Trlaxlal Stress Systems on the Strength of Rocks at Atmospheric Temperatures, Geoohvs. Jour., v. 10, 1965, p. 231-282.
34. Pfefferle, W. and Smith, C. R., Phase I Flatjack Tests, Air Force Rept. No.: SAMSO^TR-70-381, Oct. 6, 1970, 42p.
35. Obert, L., Personal communication.
36. Hoek, E., Brittle Failure of Rock, Chapter 4 in Rock Mechanics in Engineering Practice (ed. Stagg and i Zienkiewicz), J. Wiley, London, 1968, p. 99-124.
37. Wawersik, W. R., Detailed Analysis of Rock Failure in Laboratory Compression Tests, PhPD. Thesis, , University of Minnesota, 1968.
38. Cook, N. G. W., The Failure of Rock, Int. Jour. Rock Mech. Mng. Sei., y. 2, 1965, p. 389-403.
39. Houpert, R., La resistance a la rupture des granites, i Revue de 1*Industrie minerale. kaylS, 1968, p. 21-23.
40. Paulding, B. W. Jr., Techniques USed in Studying the Fracture Mechanics lof Rock, Testing Techniques for Rock Mechanics. ASTM STP 402, Am. Soc. Testing Mats., 1966, p. 73-86. ,
i i
41. Clark, G. B., Deformation Moduli of Rocks, Testing
Techniques for Rock Mechanics. ASTM STP 402, Am.
Soc. Testing Mats., 1966, p. 133-174. , ,
42. Ko, Hon-Yinn, and Scott, R. F., Deformation of Sand
in Hydrostatic Compression, Journal of the Soil
Mechanics and Foundation Division. ASCE, vol. 93,
No. SM3, l^ay, 1967.
43. Timoshenko, F., and Goodier, J. NJ, Theory of Elasticity.
McGraw-Hill Book Co., New York, 1951.
i i i < • ! i i
MT RESEARCH INSTITUTE
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-"■ -"««■»•«^"^»'^^■-'«»■W^
44. Seaman, L., and Whltnum, R. V., Stress Propagation
in Soils, Final Report-Part IV, Stanford Research
Institute, Menlo Park, California, for Defense
Atomic Support Agency, DASA 1266-4, June 1964.
45. Birch, F., and Bancroft, D., The Effect of Pressure
on the Rigidity of Rocks. Jour. Geol. v 46, nl,
Jan-Feb 1938, p. 59-87; n2, Feb-Mar 1938, p. 113-141.
IIT RESEARCH INSTITUTE
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APPENDIX A - COMPUTER PLOTS OF TEST DATA
Data was reduced and plotted using the Unlvac 1108 at
IITRI. This appendix Includes the three most significant plots
for each test, these being:
shear strain vs. deviator stress
volumetric strain vs. mean stress
axial and lateral strains vs. axial stress.
In several cases, e.g. test 19 a vs. e„, the data went off- 0 m v scale during the plotting subroutines. When this occurred, the
data was plotted at an arbitrary value within the plot scale.
The plots are arranged In order of rock type, core diameter, confining stress and test number.
Rock Tvne Diameter Confining Stress Test Page
CBG 2 5 12 A-3 10 14 A-6
15 34 A-9
4 5 9 A-12
10 11 A-15
15 19 A-18
12 5 16 A-21
5 21 A-24 5 37 A-28
10 20 A-31
32 5 27 A-34 5 28 A-37
10 29 A-40 10 30 A-43
unlaxlal strain 31 A-46
MT RESEARCH INSTITUTE
A-l
:„;;;.;;■, :': .:, ■ ■■ ■.. ■ ■.■ !' . ■■■■ ■
■■■■- ■■'..■■■ . . .
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■•.*- - :". ' .--.... ....
Rock Type
CCT
Diameter
2
12
24
nonflntng Stress Test
5 24
5 25
10 26
15 33
5 35
5 36
10 18
15 22
15 23
5 17
10 38
uniaxlal strain 32
Page
A-49
A-52
A-55
A-58
A-60
A-63
A-66
A-69
A-72
A-75
A-78
A-81
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A-2
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TEST NUMBER 12 DlfldETER 2 [N CONFINING PRESSURE 5DQQ LHflRCORL SLRCK GRRNETE
PS[
■ID.00 D.QO
SHERR iU.DD
STRAIN 20.00
MICRO-
T 3 0.Q0 M0.00
STRniNS(XlDt*2)
\ 50 .00
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TEST NUMBtR I'2 DlflflETER 2 CN CDNFINING PRESSURE 5DD0 PS I CHRRCDRL. 3LPLK üRflNITE
'-10.00 O.QQ
VOLUMETRIC
I I I I I VD.OD 20.0D 3Q.00 40.00 5D 20.0D 30.00 40.00 5D.00
STRRIN MTCRO-STRRINSCXIO**?)
I 1 I I I i i i I i I I
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TEST NUMBER
DIAMETER 2 [N CONFINING PRESSURE 5D0D LHRRCOflL BLACK GRANITE i AXIAL STRAIN
♦ LRliÄflL STRACN
PS[
•ID .00 T
0 .00 ID .00 20 .00 30.00 MD
STRREN *11CRO-STRRINS(X10^2) 0D
I 50 .00
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it
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so.oo
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TEST NUMBER DIAMETER 2 IN CONFINING PRESSURE 10000 CHflRCOflL BLACK GRANITE
-10.00 0.00 VOLUMETRIC
10.00
STRRIN 20.00 30.00 HO.00 50
MICRO-STRflINS(X10in>2) oo
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I
psr
-10.00
TEST NUMBER DIRMETER 2 tN CONFINING PRESSURE 10000 CHflRCORL BLRCK GRRNITE + RXIflL STRfltN ♦ LRTERRL STRREN
! j 1 ! !
0.00 10.00 20.00 30.00 MO.00 50.00 STRRIN MICRO-STRfiINS(X10t+2)
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TEST NUMBER 34 + DIflHETER 2 IN CONFINING PRESSURE 15000 PSI * CHflRCORL BLflCK SRRNITE +
+ +
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+
+ +
+
+ +
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■f
♦♦
+ +
^—-^j -,_ .,_ T_,— Lj *■ n ^.00 id.00 £0.00 30.00 40.00 80.00 SO .00
VOLUMETRIC STRAIN MICRO-STRflINS<X10^2)
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1
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cog
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+ TEST NUMBER 34 * OIRN^TER e IN + C0NFININ6 PRESSURE ISOOO+PSI CHflRCORL BLfltK GRRNITE + ftXIflU STRAIN A LRTERflL STRRIN
+ ++
. , - +++
+
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/
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STRAIN HlCR0H8TRniNSCX10^2) 00
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10 PS I (DRY)
CO
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500D PS I I «DR^O
-10.00 0.00 10.00 20.00 30.00 40.0C
VOLUMETRIC STRRIN MICRO-STRRINSCX10**2) 50.00
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■» LATERAL STRAIN
-10 .00 T
0.00 ID.00 20.00 30.00 H0.Ü0
STRREN M[CR0-STRRINS(X10-**2)
A-14
50.03
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TEST NUMBER QtaiETLR H [M
CQNFINENG PRESSURE iDODD CHflRCDRL 3LRLK ÜRflNITE
iO .00 0 ,00 T
iDOD 2D.DO 3000 A0 $0
SHEAR STRRIN MICRO-STRRINS(Xi0t*2)
1 50 QD
A-15
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TEST NUMBER 11 DlflMErER M [H
L'QNflNING PRESSURE iOOOO PS I LHflRLDflL 3LRCK GRANITE
■10.00 0.0D
VOLUMETRIC 00
STRRIN
I ! " I 1 20.00 30.00 MO.00
MICRO-STRRINS(X10t*2) 50 .00
1 I I }
I 1
&
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A-16
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TEST NUMBER U D I.«METER ;! :N CDNftNING PRESSURE iDDOO LHRRCDRL BuRCK GRRNITE > RXTRL STRR[N ♦ U.RTERRL STRRTN
PS I
-ID ,00 0 .00 STRPIN
i ~r 10 , oo io
M T. CRO-S TRfl INS (X1 Q t ♦ 2 ) on
—i 5 0 00
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