cannon anchorage to concrete
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I
TENNESSEE VALLEY AUTHORITY
DIVISION OF ENGINEERING DESIGN
THERMAL POWER ENGINEERING..
Civil Engineering Branch!Research and Development Staff
ANCHORAGE TO CONCRETE,
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~ ' E N N E S S E E VALlEY AUTHORITY
DI VISION OF ENGIlrEERING DF..sIGU
TlIEIU-tAL PO\'lliH ENGINEERnlG
Civi l Engineering Branch
R e s e ~ c h and Development StaffV,le. Ic"r- .J
Al"llCHORJ\GE TO CONCRETE--
Report No. CEB 75-32 ".'
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O § - - -75'- - -
ANCHORAGE TOCONCRETE
BY
Robert W. Cannon, Edwin G. Burdette, and Raymond R. Funk
The results of an anchorage research testing program undertaken by the
Tennessee Valley Authority (TVA) is described. Tests were performed to
determine the limiting load capabilities and anchorage requirements for
concrete inserts , anchor bolts, welded studs, and expansion anchors
subject to loads applied in direct tension, direct shear, and under
combined tension and shear. Three sizes of concrete inserts were tested
using various numbers of connecting bolts and different insert patterns.
Three different anchor bolt sizes and three different steels were utilized
in the anchor bolt tests . Anchorages consisted of plates embedded in the
concrete surface, (with and without shear bars) grouted plates, and plates
fastened to hardened concrete. The effect of edge conditions, strength of
concrete, size, strength, number, and spacing of anchors was found to
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Biographical Sketches
Robert W. Cannon FACI is Principal Civil Engineer, Research and Development,
Tennessee Valley Authority, Knoxville, Tennessee. Since graduating from
Georgia Tech in 1949 he has 26 years combined experience in structural
design of hydro, fossi l , and nuclear power plants and-in research. He is
a registered professional engineer in the state of Tennessee, past chairman
of ACI Committee 207, Mass Concrete and presently a member of Committees
207 and 349, Nuclear Structures.
ACI member, Edwin G. Burdette is a Professor of Civil Engineering at the
University of Tennessee, Knoxville, and a consultant to the Tennessee
Valley Authority, Knoxville, Tennessee. He received a Ph.D. from the
University of Il l inois at Urbana-Champaign in 1969 and, since that time,
has been actively engaged in research at The University of Tennessee. He
served as the Principal Investigator for the portion of th e research
- described in this paper which was performed at the University. He is
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Anchorage to Concrete
Prior to the advent of nuclear power plants th e anchorage of structural
steel· members to concrete was generally cqnsidered to be a part of the
structural steel design. The design of base plates was essentially
controlled by bearing restrict ions on the concrete; shear was transmitted
to the concrete largely through shear lugs or bars attached to the base
plate and the tensile anchorage steel was generally proportioned only for
bending or direct stress. The embedment requirements for anchorage steel
were not clearly defined by any code and were lef t largely to the discretion
of the design engineer or organization. In the design of nuclear plants
extremely large forces are generated by design basis accidents and seismic
considerations. The application of the above design approach is inefficient,
expensive, and often creates clearance and concrete placement problems
which result in bad construction details .
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anchorage systems. The third involved the effect of combined tension
and shear on the various systems.
Description of Tests
The three testing phases involved 186 individual anchorage tests consisting
of varying numbers and types of anchors and a wide variety of anchorage
conditions. The number of tests fo r the various systems are summarized
-elow. A complete description of the tests is contained in the Appendix.
A continuing program of sampling and testing both concrete and s teel
components was carried ou t for support and analysis of the anchorage
test results. Two other expansion anchor test programs are included in
the discussion, but are not l is ted in the table below.
The "standard" concrete insert is a l2-gage galvanized channel 1-3/8 inches
deep x 1-5/8 inches wide with punched anchors. The "heavy duty" insert i s
a lO-gage galvanized channel 2 inches wide x 2 inches deep with 1/2-inch
stud anchors. The "modified 3/8" insert is a l2-gage painted channel
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Number of Tests
Anchor Phase I Phase II Phase III
System Tensile Shear Combined
Load Angle
30° 60°
Standard Insert 15
Heavy-duty Insert 13
Modified 3/8" Insert 4 24 6 6
Hodified 1/2" Insert 5
5/8" Welded studs 18 5
3/4" (A307) bolts 28 17 7 4
3/4" (A307) bolts (grouted) 8
5/8" (A307) bolts (grouted) 3
3/4" (A325) bolts 2 1
3/4" (A490) bolts 2 1
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Discussion of Test Results
A complete l is t ing of the tes t resul ts are contained in the Appendix along
with load deflection curves of individual tests which were not selected
fo r inclusion with this paper.
Embedment Requirements
The peripheral shear area described in Section 11.10.2 of the 318 Building
Code is th e same area as the net resisting tensile stress area prescribed
by a 45-degree line radiating from the edge of the loaded area to the
bottom surface of the slab. I f we apply the limiting stress of
~ f ' c of section 11.10.3 to this area th e minimum embedments required to
develop th e minimum tensile strength requirement of A307 bolts (Table 2,
ASTM A307) with 3000 psi concrete would vary from 6.64 bolt diameters
fo r 1/4-inch bolts to 7.76 bolt diameters for 4-inch bolts . For
direct tensile loading of individual A307 bolts an embedment requirement
of 8 bolt diameters is therefore adequate to fully develop the tensile
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For embedment depths less than 5 inches the resisting stress cone defined
by 45-degree l ines becomes increasingly conservative with decreasing
embedment depth. This was not only demonstrated in the test results of
Phase I , but also by the pullout tests of expansion anchors by a number of
different manufacturers. Our investigations indicate a 4-degree change
in the angle of inclination for each inch of embedment depth less than
5 inches is conservative.
Tensile tests with 2-inch edge distance for th e 3/4-inch bolts and 4-l/2-inch
edge distance for the l inch A490 bolts clearly indicates that a minimum
side cover dimension is required to fullyrestrain
theside
pressure resulting
from full load transfer in bearing at the head of the bolt. A complete side
cone blowout occurred with the 19-inch embedment of th e A490 bolts leaving
the bolt embedded in the concrete with one face of th e bolt head exposed.
For deep embedments th e apparent side thrust is approximately 1/4 of the
bolts' tensile capacity. For bolts of "d" diameter located "m" distance from
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The apparent embedment requirements for shear are approximately one-half
of the requirements fo r tension based on AISC requirements for shear
connectors. Considering the effect of embedment depths less than
5 inches on the inclination of the effective pullout cone, the effective
tensile restraint force for shear connectors range from 1/4 to 1/2
of the imposed shear. If so th e cri t ical angle for anchorage would be
somewhere between 77 degrees and 63 degrees to develop the tensile
component plus 1/4 or 1/2 of th e shear component. The corresponding
resultant tensile restraint force in the concrete would be 1.03 and
1.12 times that of a pure tensile anchorage.
Discussion of Phase 1--ln the tensile testing of concrete inserts the
depth of anchorage was not a factor in any of the four different inserts
tested. When the load was transmitted to an insert through a single
l/2-inch connecting bolt , the channel lip failed by pullout. The failure
loads varied from 5.S to 8.8 kips for the standard insert which basically
agrees with the manufactures design recommendations of 2 kips per foot
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Failure Load in Kips per Foot
Insert Minimum Average High
Standard 9.2 12.2 14.9
3/8-inch studs 15 16 . 3 17.7
Heavy Duty 15.8 17.7 20.1
l/2-inch studs 16.1 18.5 20.4
On a cost per anchorage capacity basis the standard insert is probably
the least expensive and the heavy duty insert the most expensive.
In a total evaluation of anchorage requirements the increased capacity
of the modified insert with 3/8-inch stud anchors was the basis for
selection by TVA. Subsequent testing to establish welding procedures
failed to show any increased pullout capacity from the l2-gage metal for
the l/2-inch studs over the 3/8-inch studs. A broader range of
procedures and more uniformity is achieved with the 3/8-inch studs.
7-
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22 tests which were concrete f a i l u r C ! ~ , (uninfluenced by p r t ~ v i o u s tents)
the predicted fai lure loads were less than the actual fai lure loads in
19 tests . Of the 3 tests predicting higher fai lure loads, 2 had
edge conditions and the third had some indication of damage from
previous tests . The average prediction w<!s 89 percent of the actual
and the least conservative prediction was 110 percent. From this i t
can be seen that i f the normal factor of 85 percent is applied then the
predicted failure load would be less than the actual in a l l of the tests .
For the 37 tests involving fai lure of the bolt or anchor s teel the
predicted concrete fai lure loads did exceed the actual s teel fai lure loads
in 95 percent of the cases.
~ l e n the bolts or studs are spaced close enough for an intersection of
the 90 degree pullout cones, the concrete fai lure plane is always a
straight l ine between the bolt heads. The tensile strength of th e
concrete between bolts in mUltiple b o l ~ connectors is a major factor
in determining anchorage requirements. If a s teel plate is used a t
B
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30 studs in multiple stud anchorages. Material specification require
a minimum strength of 16.9 kips for a 55,0000 psi stress l imit .
We have no explanation why none of the individual stud tests met
requirements and a ll of the multiple stud tests exceeded requirements.
The average tensile strength of the I inch A490 bolts was 117 kips.
All 3 tests failed in the threads. The minimum embedment depth of
these 3 was 12.6 inches. At a minimum depth of 10.5 inches the
concrete tes t block spl i t down th e middle instead of the typical concrete
cone pullout which normally occurs. We have analyzed this as a bending
failure of th e unreinforced test block. The location of the neutral
axis and distr ibution limits of the maximum tensile bending stress in
the top surface is obviously influenced by the location of the head
of the bolt. In future tests involving minimum embedment depths of
large diameter, high strength bolts , a minimum reinforcing s teel rat io
of 0.001 is recommended.
Splitt ing faHure did not occur when 3/4-inch A-490 bolts were torqued
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concrete. Most manufacturers report data on average failure loads for
individual anchors with guidance given, by some, on the application of th e
data to spacing limitations. Our tests clearly show that unless slip
failure occurs at a lower load the maximum failure load for multiple
expansion anchors is a function of anchor spacing as described in the
embedment discussion. For expansion anchors any manufactures' claims
which exceed th e calculated concrete pullout failure load as discussed
under "embedment requirements" should be questioned.
Discussion of Phase II--The failure mechanism for shear on th e concrete
insert is shear failure of th e 1/2-inch connecting bolts for shear
perpendicular to the channel slot and continuous slip for shear along
the slot. The average shear strength of the l /2-inch bolts was 7.4
kips per bolt. The slip load is str ic t ly a function of the 50 foot
pounds of preload torque. The range of washer l i f t -of f loads in the
tensile tests (2.2 kips to S . ~ kips) is almost identical to the range
of measured slip loads in the shear tests. The average sl ip load was
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Shear testing of th e individual 3/4-inch bolts was directed principally
toward establishing th e restr ic t ions needed for edge loaded bolts . The
tests were not fully successful because the hairpin anchors which were
installed to prevent ( if possible) concrete wedge failures turned out
to be plain bars instead of deformed bars ~ n d bond fai lures occurred.
The tests did confirm the need to restrict edge shear to prevent concrete
failure. Examination of the failed wedges indicated that the entire
shearing force was transferred from th e bolt to the concrete within
1/2 bolt diameter of the surface shear plane. Applying allowable
stress to the effective tensile stress area the estimated shear wedge
failure load for an individual bolt would be:
v = 2'71(m + d/2_'2 / f 'u ta n 0) .V
o= (m + d/2) 4 + 25° 45°
Shear testing of the various 4 bolt groups established the effect of
the method of attachment on the shear strength of bolts. The average
aMI"
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at the ends of th e plate and shear bar, the load deflection curves
(figure 1) indicate most of the load is being carried by the shear
bar. The sudden transfer of load from concrete to steel a t concrete
failure was undoubtedly a contributing factor to the fai lure of the
test rig in these tests. On the other hand most of the load is
carried by the bolts prior to concrete failure for the plate without
shear bars and concrete failure apparently does not occur prior to
yielding of the bolts. The added st i ffness of the shear bar
connection prior to concrete failure does not appear to be signif icant .
The average shear strength of th e bolts with the grouted plates was
only 53 percent of th e tensile strength of representative samples.
Grout failure occurs on the front side transferring almost the
entire shear load to the back bolts. An improved bonding condition
between grout and concrete could conceivably increase the strength
of this type of connection; however, the grout pad does create an,
edge loaded condition of sorts. Unless the grout is recessed,
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percent of the individual shear tests . This strength loss is
attributed to nonuniform distribution of load due to the tensi le sl ip
characteristics of the anchors. In the individual tests the bolts
failed in shear. In the group tests failure occurred in the shank of
the anchor shell . A comparison of the relptive shear strength and
load deflection characteristics of the various bolted systems is
shown in figure 1. This shows th e shear strength of the self-dri l l ing
type anchor to be approximately 40 percent of the shear strength of the
same size of embedded A307 bolts. The shear strength of the deeper-bedded
wedge-type anchor is approximately 91 percent of the embedded A307
bolts in this comparison; however, these bolts are 21 percent higher
in tensile strength than the 307 bolts. Thus th e probable shear
strength of these anchors is 75 percent of the shear strength of
embedded bolts of the same size and materials.
Discussion of Phase III--The load producing sl ip is substantially greater
under combined loading than for shear alone in the test ing of concrete
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deflection characteristics in figure 4. When the rat io of tensile
strength to shear strength (To/Vo) for a given anchorage system is
known the resultant failure load Pu is a function of the anchorage
tensile capacity "To" and the angle of applied load "9" as follows:
Pu
=T
osin + (T Iv
)cos
o 0
Under combined loading the minimum load producing failure for bolted
connections occurs a t some angle between 25 degrees and 45 degrees
depending on To/Vo. There is also an apparent decrease in s t i ffness
of these connections underc o m b i n e d ~ l o B d s .
In these bolts the failure
stress is a combination of direct tension, bending, and the cutting
or shearing action of th e loading plate on the back side of the bolt .
Under combined loading the tensile component not only adds direct st ress ,
but l i f t s the plate off the concrete surface and thereby increases th e
bending radius and bending stress as well.
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II
(7)
(8)
The ultimate shear strength of embedded plates is dependent
entirely on th e strength of th e anchorage steel and is
relatively unaffected by th e use of shear bars when there is
sufficient anchorage steel to provide a ductile failure.
Under these conditions shear bars appear only to have a small
influence on the load a t which concrete fails on th e
frontside of th e plate. Under combined tensile and shear loads
shear bars add nothing to the st iffness characteris t ics of the
anchorage and should not be used since they create problems
in concrete placement.
Plates may be fastened to hardened concrete by preloading embedded
bolts to yield by a 2/3 turn of the nut beyond an in i t ia l snug
t ight f i t . Such connections have a shear capacity of slightly
more than 80 percent of the tensile capacity of th e bolts and
provide stiffness characteristics similar to embedded plates.
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1
(12) High bearing stress at the heads of bolts is of no consequence
as long as the side cover a t the bolt head is equal to or
(13)
greater than one half of the embedment depth. For smaller cover
distances a reduction in design yield strength may be required
(see discussion).
High bearing stresses a t the surface of the concrete also appears
to be of no consequence with bolts. As long as the distance to
the side of the block is equal to or greater than the
embedment depth of the bolt , a standard washer is a l l that is
required for bearing. (Lesser edge distances were not tested.)
(14) The use of bearing plates in the interior of the concrete to
reduce stress at the heads of bolts will require a deeper anchorage
because of the loss of the tensile strength contribution of the
concrete between bolt heads in resisting pullout. They are
no t recommended since they perform no useful function and only
17
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18
(18) For expansion anchors with embedment depths of 4 bolt diameters
or less, shear strength appears to be influenced by th e pullout
strength of the concrete even though failure in single bolt tests
occurs in the bolt.
(19) Larger safety factors must be utilized with expansion anchors
to l imit deflections to those commensurable to bolted
connections.
II,
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RH EXP. ANCHOR(3&" DEEP)
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0.0 0.1 0.3 O.Q. 0.5 0.6
DEFLECTION INCHES
FIGURE 1
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CONCRETE INSERT
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FIGURE 2:.
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COMBINED LOADING
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FIGURE 4
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Anchorage to Concrete
APPENDIX
Phase I (Tensile Tests)--The f i r s t series of tes ts were performed on two
commercially available concrete inserts , on 3/4-inch A307 anchor bolts , and
on SIS-inch welded studs.
The bolts were tested at varying depths and edge distances and the studs
were tested for the effects of number, spacing, and anchorage pattern. The
heavy duty insert was a 2-inch by 2-inch la-gage stee l channel and the
standard insert was a l-3/S-inch by 1-S/S-inch 12-gage steel channel.
The various anchorages were embedded in 30-inch square by 4-foot long
test blocks util izing as many faces as possible to reduce the number of
test blocks required and to reduce the variable effect of concrete
strength. The testing apparatus consisted of a 50-ton calibrated
hydraulic jack with a loading beam to spread the reaction loads to a
19
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I-20
1 The 3/4-inch A307 bolts were embedded to depths varying from 4 inches to
18 inches with edge distances varying from 2 inches to 6 inches, but
not more than the embedded depth. All 18 bolts were embedded in a single, test block. As a resul t , some of the concrete failures influenced the
test results of others and a second series of 10 bolts were tested. With
I the exception of one test each in the center of the block for 3-inch and
I 4-inch embedment depths, th e remaining eight tests were run with 2-inch and
3-inch edge distances. Only one test out of this group was apparently
iinfluenced by concrete failure of prior tests.
J
The in i t ia l testing of the S/8-inch welded studs consisted of four single-
stud pull tests , eight double-stud pull tes'ts at 4-inch through 8-inch
t spacing, and one test with four studs at a 4-inch spacing in a square
pattern. All studs were welded to 3/8-inch thick plates. Some of the
t pull bars, required for attaching the test r ig, were welded to the
t3/8-inch plates prior to embedment and some af ter embedment to check
the effects of welding on the anchorage. In some instances th e welding
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roughen th e slick surface of the holes in th e limestone aggregate concrete
resulted in bond failure with both epoxy and portland cement grouts in the
ini t ia l tests . Tests were repeated with a minimum of surface roughening
and no bond failures occurred. Each series consisted of 8 tests for
embedment depths of 4, 5, and 6 inches w i ~ h edge distances of 2 and 3
inches to the center of th e bolts.
Additional pull tests were performed using I-inch diameter high strength
(ASTM A490) bolts to determine what effect , i f any, the higher bearing
stress a t the head of these bolts had on embedment requirements. These
bolts were tested in 3-foot by 3-foot by 3-foot concrete blocks. One
block was cast with six bolts of varying depths with one bolt in the
center of each face. In the other block four bolts were cast one in each
face with 4-1/2-inch edge distances. An increase in the size of
test rig was required for these tests.
Phase II (Shear Tests)--The tests for both Phase II and Phase III were
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device is a Linear Variable Differential Transformer (LVDT). The
test apparatus thus has th e abil i ty to imput either load or deflection
and to measure both.
Special connecting devices were designed for the various types of anchorages
to be tested. The devices were pin connected to the loading rig such
that the center of the loading pin and the desired plane of shear could be
aligned. The st i ffness of the beams through which th e load was transmitted
from loading pin to test block was such that essentially no rotation
occurred for the normal loading conditions achieving very close to pure
shear conditions.
The fixed height of the testing apparatus established a maximum test block
dimension of 27 inches. The test block was therefore cast as a 27-inch
cube in order to util ize as many faces of each block as possible. The shear
load in the test block was transmitted back to the test r ig through bearing
on the forward face of the test block. The moment induced in the block
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run with 4- and 8-bolt connections for shear applied a t IS, 30 , and 45
degrees to th e principal axis of the cross.
23
A total of five shear tests were performed on groups of S/8-inch studs welded
to 3/B-inch plates and embedded in the 27-inch cubical blocks. Three of
these tests were on groups of two, three" and four studs spaced in a single l ine
pattern on 4-inch centers. The other two tes ts were on groups of four in a
square pattern with one group spaced on 4-inch centers and the other on
6-inch centers.
In the f i r s t series of shear tests with the 3/4-inch bolts only th e bolts
were embedded in the concrete. Four single bolts were tested for edge
effects on shear, two with 3-inch edge distance and two with 6-inch edge
distance. In addition, two groups of four bolts in a square pattern on
8-inch centers were tested. All bolts were embedded 6 inches deep and
the loading plates were fastened to the hardened concrete without
grout. Half of the plates were fastened under "finger t ight" conditions
and half were preloaded by the AISC "turn-of-the-nut" method. Additional
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IIIIIIIII
A third series of four-bolt configurations was tested using ASTM A325 and
A490 bolts with the plates fastened to hardened concrete and the bolts
preloaded to yield as in the f i rs t series.
Two types of 3/4-inch expansion anchors were tested in shear using the
same grouping pattern as the bolts. Similar anchors are manufactured by
a number of different concerns and are commonly used. The sel f -dr i l l ing
type anchor uses i t s own shell as a dri l l bit and accomplishes i ts anchorage
by driving the shell down over a wedge which expands th e shell base. These
anchors have a I-inch outside shell diameter and 3-1/4-inch embedment.
Connections to these anchors was made with 3/4-inch A307 bolts . The
other type of anchor requires a special dri l l b it to control hole size
and achieves i ts anchorage by wedges on each side of th e bolt which
expand when the bolt is tightened. These bolts are made of high strength
steel and can be purchased in different lengths. The bolts tested in
this series were set 6 inches deep.
24
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25
A total of seven tests were performed at a 30-degree load angle on the
basic four-bolt configuration using 3/4-inch A307 bolts with embedded plates
(with and without shear bars), grouted plates, and plates fastened to
hardened concrete. Only four tests were performed with 3/4-inch bolts a t
a 60-degree load angle because of unexpected block fai lures and because
of expiration of ~ h ~ contract completion date. Three additional tests
were performed at the 60-degree loading on 5/S-inch bolts fastened to
hardened concrete. These bolts were set by drill ing into existing
blocks and set with an expansive grout. They were set a t 3-1/2-inch,
7-inch, and S-inch depths. (Tests were also planned a t 5-inch and
6-inch depths but could not be performed because the bolt alignment
did not match the holes in the connecting plate. The end of the
school year and expiration of the contract did not allow time for
I retest .)
A total of five tests were performed with expansion anchors at a load
angle of 30 degrees. Two of these were performed on the self-dri l l ing
.,......
- -- J-'!J P'iiiif till..
Table I
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-- - - - -Tension Tests
Concrete Failure
Number Size Embed Edge Spacing f 'c Failure LoadInches Depth Distance Inches psi Actual Estimate Es t Remarks
Inches Inches 1000 lb . 1000 lb . Act.
1 3/4 3 15 3500 16 11. 7 0.73 A3074 2 4870 9.9* 14.3 Embedded4 2 4315 16.6 13.5 .81 Bolts
4 3 4870 13.3* 16.4
4 3 4315 18.3 15.4 .844 4 4870 19.9* 18.1 .91
4 15 4315 25.4 17.5 .69
5 2 4635 14.5 16.0 1.10
5 2 3500 14.9 13.9 .93
5 3 4635 20.5 18.3 .895 4 4635 22 20.3 .92
6 2 4635 22.7 2h2 .93
6 2 3500 17.7* 19.0
6 3 4315 28.2 23.9 .85
7 2 5050 23.8* 29.7
1 3/4 5 2-3/4 5500+ 23.2 19.4 .84 A307
7 1-1/4 5500+ 22.1 19 .86 Grouted4 2-1/4 5500+ 14.4 15.75 1.10 Bolts
4 2-1/4 5500+ 16.6 15.75 .95
4 5/ 8 6-3/8 16 2 4000 59.7 46.2 0.77 WeldedI I 15 3 4000 63 53.9 .86 Studs14 4 4400 63.4* 65.5 1.03
1 1 10.5 18 4300 98 90.8 .93 A490
18.9 4-1/2 4245 94 76.3 .82 Bolts
16.8 4-1/2 4300 82 76.8 .9414.7 4-1/2 4300 82 76.8 .9412.6 4-1/2 4300 76 76.8 1.01
,.1 ••
. * Concrete damaged from previous tests:, :
. III' • til •
. , . .• •
..• •
..
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Number
1111222
22222222
24
SizeInches
5/ 8
EmbedDepthInches
6-3/8
EdgeDistance
Inches
+7
Table 2(a)
Tension Tests
Steel Failure
SpacingInches
222
334455668
84
f 'epsi
4635505048704635431543154315350035004635463550505050487048704635
46355050
Failure LoadActual Concrete Unit Remarks1000 lb. (Estimate) 1000
1000 lb. lb/bolt
16 34.8 16 Welded15.5 36.3 15.5 Studs
16.4 35.6 16.4
16.5 34.8 16.5
40.9 40.2 20.5
39.2 40.2 19.6
35.4 40.2 17.7
34 43.6 1738.1 43.6 19.1
36.5 48.7 18.3
36.5 48.7 18.3
34.8 54.4 17.4
38.1 54.4 19.1
39.3 57 19.7
36.5 57 18.3
37 62.5 18.5
35 62.5 17.574 69.8 18.5
---, -
...
_ _...............
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Uumber
1
1
1I" .
Size
Inches
3/4
3/4
1I
Embed
DepthInches
56666
77788
56678
8
12.6
14.7
16.8
Table 2
Tension Tests
Steel Failure
EdgeDistanceInches
53456
24524
3-3/42-1/2
32-3/4
2-3/4
2-3/4
181818
SpacingInches
f 'c
psi
46355050505050505050
40005050505035003500
5500+5500+5500+5500+5500+
5500+43004245
4200
Failure Load
Actual Concrete Unit Remarks1000 lb . (Estimate) 1000
1000 lb . lb/bo1t
21 21.4 21 A(307)26 25.9 26 Embedded
26.1 28.6 26.1 Bolts26.1 30.9 26.126.2 32.1 26.2
25.4 26.5 25.426.3 36.9 26.329.6 39.9 , 29.623.2 31.3 23.224.4 46 24.4
29.9 21. 7 29.9 A(307)25.4 25.4 25.4 Grouted26 27 26 Bolts30.4 34 30.429.3 42.6 29.3
27.742.6
27.7116 130.8 116 A(490)118 176.8 118 Bolts
118 229.7 118
JUiJ.L . : . . . ~
- -' J!!'!I!!....
....
.- @!!Ii. @!!I!IIJ 1iIh,..
Table 3
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Tension Test
Concrete Inserts
Connecting Length End Washer Failure Load TypeBolts of Anchors Lift-off Total Per Foot of
No. Spacing Channel Yes No FailureInches Inches kips/bolt 1000 Ib 1000 lb
1-5/8 x 1-3/8 Standard Insert
1 48 x 3.3 5.5 LP48 x 3.9 8.3 LP
48 x 2.2 8. 8 LP
* 48 x 4.4 5.3
* 48 x 5.5 8.4 LP
* 48 x 5. 5 8. 1 LP2 3 12 x 4. 2 10.7 AT
3 6 24 x 4.4 17.3 11.5 AT ,
4 3 14 x 3.2 16 16 AT4 3 12 x NM 14.9 14.9 AT
4 3 12 x 2.6 11.6 11.6 AT
6 3 24 x NM 14.9 9. 9 AT
6 3. 24 x NM 13.8 9. 2 AT
2 x 2 Heavy Duty Insert
1 3 24+ x NM 9.7 LT
2 3 18 x 15.5 LT
3 3 12 x 17 .2 17.2 LT3 6 12 x 16.6 16.6 LT
3 6 24 x 24.7 16.5 LT3 3 24 x 30.1 20.1 LT3 3 12 x 18.3 18.3 LT
4 3 12 x 16.6 16.6 LT.4 3 16 x 18.8 18.8 LT6 3 18 x 23.8 15.8 ST6 3 20 x 26 17.3 LT6 3 20 x 29 19.3 LT
*Edge Load
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Description of Failure
LP - Pullout of LipLT Tear of Lip
ST - Stud tear from channel web
AT - Anchor tear from channel web
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----
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Number Size
1 3/4
1 3/41 3/41 3/4
1 3/4
1 3/4
1 3/4
1 3/41 3/4
1 3/41 3/41 3/4
4 3/4
4 3/4
4 3/4
4 3/4
4 3/4
4 3/44 3/4
2 5/83 5/84 5/ 8
'.,: : 4 5/8
. 14 5/8
!
..
---- ._-- '., - ..
EmbedDepth
6666666
66666
66666
(A325)(A490)
StudsStudsStudsStudsStuds
EdgeDistance
36363-1/84-3/16
56-3/167-3/8
8-3/169-5/16
10-3/4
'Table 4 '
Shear Tests
Spacing
(A307 Bolts)
88888
44444
f lc
5600570056005800382538255080
37004100410045504600
46004500535051004450
24002400
60004500500045003900
Concrete
1000 1bs
11
1117
91820
407076
6060
Failure LoadSteel Per Anchor Remarks1000 1bs kips/bolt
04 HPA
22 22 06 HPA
22 22 fl6 HPA
20 20 fl4 HPA
fJ6 HPA18 18 fJ6 HPA
20 20 06 HPA
18 18 #6 HPA
24 24 #6 HPA
19 . 19 fl6 HPA
18 18 fl6 HPA
25 25 fl6 HPA
85 21.3 SM
87 21.8 SM
6 16 GP
110 27.5 EP
112 28 EP & SB
182 45.5 SM
183 45.8 SM
36 18 EP
51 17 EP
67 16.8 EP
73 18.3 EP
65 16.3 EP
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' ~ : : : ; ; ~ ; . J ~ . ' : ~ ",.";; ....
1 •
' ..
. : . ,>"'! '. ' ••
Number
444
Size
3/43/4
3/4
HPA Hairpin anchorGP Grouted plateSB - Shear BarEP - Embedded plate
EmbedDepth
3-1/43-1/46
SM - Surface Mounted Plate
Table 4 (Continued)
EdgeDistance
(Exp.)
(Exp.)(Exp. )
Shear Tests
Spacing
(A307 Bolts)
8
88
f lc
555056004550
Concrete
1000 lbs
Failure LoadSteel Per Anchor
1000 lb s kips/bolt
44.4
49.6100
11.112.425
Remarks
SM
SM
8M
-
Table 5
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Number
of
ConnectingBolts
22334
455
22334
455
4448
12
Direction
of
Load
Perpendicular
toslot
Longitudinal
to
slot
Cross
Connections
Concrete Inserts
Shear Tests
Anglewith
PrincipalAxis
Degrees
0
0
0
of Loadwith
Face ofBlock
Degrees
0
Average
0
Average
0
Average
Maximum LoadTotal Per Bolt
Kips Kips
14 716 821 726 8.729 7.3
26 6.536 7.2
39 7.8
7.4
5 2.511 5. 5
6 26 2
12 314 3.516 3.2
26 5.2
3.36
18 4.522 5.5
26 6.540 565 5.4
5.38
{
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Number
ofConnectingBolts
8484
84234
234
2
34
234
DirectionofLoad
Cross
Connections
Longitudinalto
slot
Table 6
Concrete Insert
Shear and Combined Load
Angle of Loadwith with
Principal Face ofAxis Block
Degrees Degrees
45 045
30
30
1515
0 30
0 30
0 60
0 60
Haximum LoadTotal Per Bolt
Kips Kips
50 6.2524 6.052 6.528 7
51 6.3720 5
11.5 5.7511.5 3.83
17.5 4.38
9 4.516 5.33
15.5 3.88
13.8 6. 9
15.6 5.217.75 4.37
13.5 6.73
13.6 4.5319.6 4.9
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A307
30S8 SHEAR BAR
EP EMBEQDED PLATE.GP GROutED PLATE
20(I)
Q.
!lie
!30
=Q:
IJJQ.
Qoct0
10'
Ii·o
0.0 0.1 0.2 0.3 O.q. 0.5
\DEFLECTION INCHES
FIGURE 5
i:,;
.
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.-
,; .
J.)'
CI )
4.
lie:
...J0m
0::
UJ
4.
Q
-<0...J
-.'
50
qO
SO
20
10
o
0. 0 0.1
DEFLEctiON INCHES
A325, Aq90, EXP ANCHORS
KB EXP. ANCHORf::J0 (6" DEEP)
~ \ l c ~ O : .......
RH EX', ANCHOR......'" (a. DIE'),
K8 @ S O O ~ -----_ .... -.. ..-.,
0.'"
F,IGURE 6
"I
-',- .',
--
--
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8
6
2
oiiI
\
\1I i;> .,
0.0
DEFLECTION INCHES
O. I
.. .-.. ' ~ ~ '
..
INSERT CROSS CONNECTIONS
0.3
FIGURE 7
.'1,' ".'
", '.