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Lecture 4
Design of
Rock-socketed Piles
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Rock-socketed piles
PILE
Rock
Socket
Soil
Rock
Load
In most cases, the lower part of the pile is socketed into rock.
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Performance of rock socket
Socket friction
Socket friction increases with socket
roughness
Smooth socket friction fully mobilisedat small pile settlement
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(after Horvath & Kenny, 1979)
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Performance of rock socket
Socket friction is related to socket
roughness
Horvath et al. (1983) established that
fs = 0.8 (RF)0.45 qu
where RF = roughness factor = (r Lt)/(D
L)
r = average height of asperities, Lt = total
distance along the socket wall profile, D =
socket diameter, L = socket length & qu =
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Effect of socket diameter Seidel & Harberfield (1995) found that
as the socket diameter increases, the
effect of dilation is reduced for a given
degree of socket roughness. The variations in socket friction can
be changed by a factor of up to 3, fordiameters varying between 0.5 m and
2 m.
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Rock socket frictionUnit shaft friction fs
Early days (1960s to early 1970s)
fs = 250 kPa for fragmented shale
fs = 120 to 180 kPa for weak
mudstone
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Rock socket frictionfs is related to qu
Rosenberg & Journeaux (1976)
fs = 0.375 (qu)0.515
Meigh & Wolshi (1979)
fs = 0.22 (qu)0.6
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Rock socket friction Williams & Pells (1981)
fs = qu
where and are reduction factors
reflecting rock strength and fracturestate, respectively. See Figures.
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Williams & Pells (see next figure for value of )
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(after Williams and Pells)
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Rock socket friction Horvath et al. (1983)
fs = 0.2 to 0.3 (qu)0.5
Rowe & Armitage (1987)
fs = 0.45 (qu)0.5 for a smooth socket
fs = 0.60 (qu)0.5 for a rough socket
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Rock socket friction From a large set of field data
(including those of Singapore),
Zhang & Einstein (1998) found that
fs = 0.4 (qu)0.5 for a smooth socket
fs = 0.8 (qu)0.5 for a rough socket
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Rock socket frictionRecommendations for local design
Preliminary design using Horvath
fs = 0.2 to 0.3 (qu)0.5
Detail design using Williams & Pells
fs = qu(All values need to be confirmed by load tests)
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Performance of socket base
For the same rock strength, base
resistance increases with overburdenpressure
Shallow embedment: brittle failure Deep embedment: ductile failure (i.e.
capacity is not a problem, only
settlement is a concern, see figure)
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Socket base resistanceUnit base resistance qb
Early days (60s & 70s)
Weak shale 3 MPa
Moderately strong shale 3.9-4.9
MPa
Weak mudstone 6.8 MPaModerately strong mudstone 28-58
MPa
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Correlation
between qband RQD
for a jointed
rock mass(after
Peck et al.,
1974)
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Socket base resistance Teng (1962)
qb = 5 to 8 qu
Coates (1967)
qb = 3 qu
Tomlinson
qb = 1 to 6 qu
(depending on rock fracture state)
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Socket base resistanceRecommended approach for design
Rowe and Armitage (1987)
qb = 1 qu under working stress to
ensure no yielding of rock
qb = 2.5 qu under ultimate condition
[Values subject to capacity andsettlement verification from load tests]
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Socket base resistance Based on a large number of field data
(including that of Singapore)
Zhang & Einstein (1998) found that
qb = 3.0 to 6.6 (qu)0.5
(with a mean coefficient of 4.8)
[Note qb is related to square root ofqu]
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Zhang & Einstein (1998)
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Conservative ratio of qb upon qu
(after HK GEO)
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(after HK GEO)
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Unconfined compressive strength
REMINDER
Use quc (unconfined compressive
strength of concrete) if the rock is
stronger than concrete.Poser: In view of the above, is it
necessary to socket pile into hard rock?{Answer can be yes or no!}
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Settlement of rock-socketed piles
For socketed piles with long
embedment length, capacity isnormally governed by concrete
strength. Settlement of pile needs to be
evaluated especially in suspected soft
toe cases.
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Rock socket Under working load, the load-
settlement response of a socketedpiles is fairly linear in most cases.
Elastic theory can be employed toevaluate the pile settlement
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0 4 8 12 16 20
Load (MN)
0
4
8
12
16
Settlem
ent(mm)
Load-settlement response is reasonably linear up to working load of 10 MN
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Rock socket modulus Er Tomlinson
Er= j Mr quc (see tables)
Rowe and Armitage
Er= 215 (qu)0.5
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Mass factor j (after Tomlinson and BS8004)
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Modulus ratio Mr (after BS8006)
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Settlement of rock socket RECOMMENDED APPROACH
Rowe & Armitage (1987)
Assumptions:
Soil above rock socket has nosignificant contribution in resistance
Elastic solutions are developedassuming a fully bonded socket using a
FEM.
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(after
Rowe &Armitage,
1987)
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Rowe and Armitage Assumptions (continued)
The dimensionless settlement I defined
by I = Ed D/Qt
where is the socket settlement, Ed isthe design socket shaft modulus, D is
socket diameter and Qt is the working
load. Design charts are developed for various
pile geometry and socket/concrete
modulus ratios
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Rowe and ArmitageDESIGN CONCEPT
Satisfying a user-specified design
settlement
Ensuring an adequate factor of safetyagainst failure
Limit state design concept: partial safety
factors applied to deformation andstrength parameters
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Rowe and ArmitageDESIGN PROCEDURES
Step 1: Given
design settlement d
socket diameter D applied working load Qt
Concrete modulus Ep [Factored] Unconfined compressive strength of
rock qu
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Rowe and Armitage Step 2 (a): Determine
fs = 0.45 (qu)0.5
Er= 215 (qu)0.5
Determine Eb
if qu
at pile base is different
Step 2(b):Apply partial factor of safety
Design unit shaft resistance d = f fs
Design rock mass modulus Ed = fE Er
Partial factors f and fE are taken as 0.7 or 0.5(for probability of 30% and 11% exceeding d )
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Rowe and Armitage Step 3: Determine Ep/Ed and Eb/Er
Step 4(a): Determine maximum
socket length assuming no base
resistance(L/D)max = Qt/( D
2 d)
Step 4(b): Determine thedimensionless settlement I
I = Ed
D/Qt
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Rowe and Armitage Step 5(a): Determine (L/D)d and
(Qb/Qt)d from the intersection of thefactored design line for (L/D)max with
the contour for Id using design chartsallowing for slip
Step 5(b): If there is an intersection,
calculation is okay & proceed to step
6.
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Qb =100%,
I.e.
Full base
resistance
Qb = 0%, I.e. Full shaft resistance
Intersection
refers to
estimated
Qb(after
Rowe &
Armitage,1987)
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Rowe and Armitage Step 5(C): Determine the value of (L/D)d
for given Id If there is a value of (L/D)d can be found,
determine (Qb/Qt)d for the (L/D)d and proceed
to step 6 If there is no value, redesign is necessary, go
back to step 1.
Refer to paper for details for design involvinga recessed pile
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Determine the
value of (L/D)dfor given Id
Elasticsocket
(no slip)
(after Rowe &
Armitage, 1987)
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If there is a value of (L/D)d can be found,
determine (Qb/Qt)d for the (L/D)d
(after Rowe & Armitage, 1987)
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Rowe and Armitage Step 6: Check for base condition
qt = Qt/( D2/4)
Under working load
qb = (Qb/Qt)d qt and need to be < qu Under worst condition
qbu
= qt
- 4(L/D)d
(0.3 fs
) and < 2.5 qu
assuming only 0.3 fs can be mobilised
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Summary
of designcurves
(1) Full slipEb/Er = 0.5
(after
Rowe &
Armitage,
1987)
Fig. 6.1
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Summary
of designcurves
(2) Full slipEb/Er = 1.0
(after
Rowe &
Armitage,
1987)
Fig. 6.2
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Summary
of designcurves
(3) Full slipEb/Er = 2.0
(after
Rowe &
Armitage,
1987)
Fig. 6.3
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Summary
of designcurves
(4) Elasticsocket
(No slip)
(after
Rowe &
Armitage,
1987)
Fig. 6.4
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Summaryof design
curves
(5) Elastic
socket:
baseresistance
(after
Rowe &Armitage,
1987)
Fig. 6.5
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Axially loaded rock-socketed piles
Examples 4.1 [from Rowe & Armitage Page 138 Case
(i)]
Given:
Design settlement d = 8.5 mmPile diameter D = 0.71 m
Design working load Qt = 4.45 MN
Modulus of pile material Ep = 37,000 MPa
Unconfined compressive strength of rock qu = 6.75 MPa
[Rock at pile base is more fractured and Eb = 0.75 Er]
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CalculationStep 2(a): Unit shaft friction fs = 0.45 (qu)
0.5 = 1.17 MPa
Youngs modulus of rock Ef= 215 (qu)0.5 = 560 MPa
Step 2(b): Take partial factor of safety f = fE = 0.7[Probability of 30% not exceeding d]Design unit shaft friction d = f fs =0.82 MPaDesign rock mass modulus Ed = fE Er= 390 MPa
Step 3: Ep/Ed = 95 (therefore use Ep/Ed = 100 chart)Eb/Er= 0.75 (interpolation between Eb/Er =1 [Fig. 6.2]
and = 0.5 [Fig. 6.1])
Step 4(a):Assume no base resistance, maximum socket length
(L/D)max = Qt / (D2 d ) = 3.4
Step 4(b): Dimensionless settlement I = Ed D/ Qt = 0.53
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Calculation (cont.)Step 5(a):
By drawing a line from (Qb/Qt)d = 100 % to (L/D) = 3.4in Fig. 6.2(d) (i.e. for Eb/Er= 1) show that (Qb/Qt)d =63 % and the corresponding design socketlength/diameter ratio (L/D)d = 1.3 for Id = 0.53.
Similarly for Eb/Er= 0.5 from Fig. 6.1(d),(Qb/Qt)d = 27 % and (L/D)d = 2.5
By interpolation, (Qb/Qt) = 45% and (L/D)d = 1.9
Hence design socket length = 1.9 D = 1.35 mand proceed to Step (6)
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Calculation (cont.)Step (6) Unit loading pressure
qt = Qt / (D2
/4 ) = 11.2 MPa Under working condition, allowable base pressure
qb = (Qb/Qt)d qt = 5.1 MPa < qu OKAY
Under worst condition where only 0.3 fs can bemobilised qbu = qt 4(L/D)d (0.3 fs)
= 8.5 MPa < 2.5 qu OKAY
Design completed and required socket length is
1.35 m.
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Example 4.2Given:
d = 5 mm, D = 1 m, Qt = 7.8 MN,Ep = 34,000 MPa, qu = 20 MPa, Eb = Er
Calculations:
Step 2(a) & (b): d = f fs = 0.7 x 0.45 qu = 1.4 MPa
Ed = fE Er= 0.7 x 215 qu = 673 MPa
Step 3: Ep/E
d= 34,000 / 673 = 50
Step 4: (L/D)max = Qt / (D2 d ) = 1.77
I = Ed D/ Qt = 0.43
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Calculation (cont.)Step 5(a): Fig. 6.2(c) No intersection!
Step 5(b): Fig. 6.4(a)
for I = 0.43 & Ep/Ed = 50
(L/D) required 1.2
Fig. 6.5(a)for (L/D) = 1.2 & Ep/Ed = 50
(Qb/Qt) = 30%
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Calculation (cont.)Step 6: qt = Qt / (D
2 /4 ) = 9.93 MPa
Under working conditionqb = (Qb/Qt)d qt = 0.3 x 9.93 MPa = 2.98 < qu
(20MPa) OKAY
Under worst working conditionqbu = qt 4(L/D)d (0.3 fs)
= 9.93 4(1.2) (0.3 x 0.45 qu)
= 7.03 MPa < 2.5 qu OKAY
Required socket length = 1.2 x 1 = 1.2 m
and there is no slip in the socket.
References for
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References for
Design of rock- socketed piles
Related publications by C F Leung1. Leung C F and Radhakrishnan R (1985). Observations of an
instrumented pile-raft foundation in weak rock, Proc. 11th Int.Conf. on Soil Mech. and Fdn. Engr., San Francisco, pp. 1429-1432.
2. Leung C F, Radhakrishnan R and Wong Y K (1988).
Observations of an instrumented pile-raft foundation in weakrock, Proc. Instn. Civ. Engrs., Part 1, Vol. 84, pp. 693-711.
3. Leung C F and Radhakrishnan R (1990). Geotechnicalproperties of weathered sedimentary rocks, GeotechnicalEngineering, Vol. 21, pp. 29-48.
4. Leung C F, Radhakrishnan R and Tan S A (1991).Performance of precast driven piles in marine clay, J. ofGeotech. Engr., ASCE, Vol. 117, pp. 637-657.
5. Leung C F (1996). Case studies of rock-socketed piles,Geotechnical Engineering, Vol. 27, pp. 51-67.
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Related publications by C F Leung (cont.)
6. Leung C F and Tan G P (1996). Load carrying capacity of spunpiles, Proc. 12th Southeast Asian Geotech. Conf., Kuala Lumpur,Vol. 1, pp. 423-428.
7. Leung C F and Chow Y K (1998). Settlement of rock-socketedpiles, Proc. 5th Int. Conf. on Tall Buildings, Hong Kong, Vol. 2, pp.884-889.
8. Radhakrishnan R, Leung C F and Subrahmanyam R (1985).Load tests on instrumented large diameter bored piles in weak
rock, Proc. 8th Southeast Asian Geotech. Conf., Kuala Lumpur,Vol. 1, pp. 2.50 2.53.
9. Radhakrishnan R and Leung C F (1989). Load transfer behaviourof rock-socketed piles, J. of Geotech. Engr., ASCE, Vol. 115, pp.755-768.
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Other publications
1. BSI (1986). British Standard Code of Practice for Foundations(BS8004:1986), British Standards Institution, London, UK.
2. Cole K W and Stroud M A (1977). Rock socket piles at
Coventry Point, Market Way, Coventry" Piles in Weak Rock,Instn. of Civil Engrs., UK, pp. 47-62.
3. GEO (1996). Pile Design and Construction, GEO PublicationNo. 1/96, Geotechnical Engr. Office, Hong Kong.
4. Horvath R G and Kenny T C (1979). Shaft resistance of rock-
socketed drilled piers, Symp. on Deep Foundations, ASCE,pp. 182-214.
5. Horvath R G, Kenny T C and Kozicki P (1983). Methods ofimproving the performance of drilled piers in weak rock, Can.Geotech. J., Vol. 20, pp. 758-772.
6. ISRM (1985). Suggested method for determining point loadstrength, Int. J. of Rock Mech. and Mining Sci., Vol. 22, pp.51-60.
7. Irfan T Y and Powell G E (1991). Foundation Design ofCaissons on Granitic and Volcanic Rocks, GEO Report No. 8,
Geotech. Control Office, Hong Kong.
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Other publications (cont.)
8. Lam T S K, Yau J H W and Premchitt J (1991). Side resistance ofa rock-socketed caisson, Hong Kong Engineer, Vol. 19, No. 2,pp. 17-28.
9. Meigh A C and Wolski W (1979). Design parameters for weakrock, Proc. 7th European Conf. On Soil Mech. and Fdn. Engr.,Brighton, Vol. 5, pp. 59-79.
10. Osterberg J O and Gill S A (1973). Load transfer mechanism forpiers socketed in hard soils on rock, Proc. 9th Canadian Symp. on
Rock Mech., pp. 235-262.11. Peck R B, Hanson W E and Thornburn T H (1974). Foundation
Engineering, 2nd Edition, John Wiley and Sons, New York, USA.
12. Rosenberg R K and Journeaux N L (1976). Friction and endbearing tests on bedrock for high capacity socket design,
Canadian Geotech. J., Vol. 13, pp. 324-333.13. Rowe R K and Armitage H H (1987a). Theoretical solutions for
axial deformation of drilled shafts in rock, Canadian Geotech. J.,Vol. 24, pp. 114-125.
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14. Rowe R K and Armitage H H (1987b). A design method for drilledpiers in soft rock, Canadian Geotech. J., Vol. 24, pp. 126-142.
15. Seidel J P and Harberfield C M (1994). A new approach to theprediction of drilled pier performance in rock, Proc. Int. Conf. onDesign and Construction of Deep Foundations, Orlando, Vol. 2,pp. 556-570.
16. Shiu Y K and Chung W K (1994). Case studies in prediction andmodelling of the behaviour of foundation on rock, Proc. 8th Int.
Congress on Rock Mech., Tokyo, Vol. 3, pp. 1243-124.17. Teng W C (1962). Foundation Design, Prentice-Hall, USA.
18. Tomlinson M J (1995). Foundation Design and Construction, 6thEdition, Longman, UK.
19. Williams A F and Pells P J N (1981). Side resistance rock
sockets in sandstone, mudstone and shale, Can. Geotech. J.,Vol. 18, pp. 502-513.
20. Zhang L and Einstein H H (1998). End bearing capacity of drilledshafts in rock, J. of Geotech. and Geoenvir. Engr., Vol. 124, pp.574-584.
Other publications (cont.)