footing response to horizontal vibration
TRANSCRIPT
FOOTING RESPONSE TO HORIZONTAL VIBRATION
By M. V. Nagendra1 and A. Sridharan2
INTRODUCTION
Resonant frequency and resonant amplitude are the two important criteria involved in the design of foundations subjected to periodic loading. The effect of the type of contact pressure distribution and the displacement condition are of importance while predicting the dynamic response of footings (2,4,7,9). Elastic half-space model has been used by many investigators (1,3,5,6,11) to predict the dynamic response. Bycroft (1) obtained solution for the response of a rigid circular footing subjected to t frequency dependent horizontal excitation, considering weighted average displacement, assuming that the vertical displacement due to horizontal load is zero. Luco and Westmann (6) obtained the Fredholm integral equations governing the response of a rigid circular footing, assuming that the vertical stress due to the horizontal load is zero. It can be seen from literature that for horizontal vibration, solutions are i available only for rigid base shear distribution for weighted average dis- \ placement condition. However, because the relative rigidity of footing ! and soil is bound to vary, different types of shear distributions are inevitable in actual practice, as have been well established for vertical vi- ] bration. Therefore, in this paper, solutions have been obtained for the cases where solutions are not available, considering three types of contact shear distributions; rigid base, uniform and parabolic and three displacement conditions; central, average and weighted average. It has been j assumed that the vertical stress developed due to horizontal dynamic force is zero (6,11).
Analysis.—From the equations of motion of a linear elastic medium, in cylindrical coordinates, the solution for the displacement components, u, v, and w in r, 0 and z directions was obtained by Sezawa (10). \ Considering the case where an oscillator is acting upon the surface of a semi-infinite solid, and if the oscillator is replaced by a contact shear force of amplitude, Px, with frequency, co, acting at the surface (z = 0), the boundary conditions for the three types of contact shear distribution I may be written as follows: I
(a) Rigid base contact shear distribution:
az = 0 (la)
Pxeiat !
T* = o—71 ~s c o s 8 for /• < a ^
'Research Scholar, Dept. of Civ. Engrg., Indian Inst, of Science, Bangalore 560 012, India.
2Assoc. Prof., Dept. of Civ. Engrg., Indian Inst, of Science, Bangalore 560 012, India.
Note.—Discussion open until September 1, 1984. To extend the closing date one month, a written request must be filed with the ASCE Manager of Technical and Professional Publications. The manuscript for this paper was submitted for i review and possible publication on January 28, 1982. This paper is part of the Journal of Engineering Mechanics, Vol. 110, No. 4, April, 1984. ©ASCE, ISSN \ 0733-9399/84/0004-0648/$01.00. Paper No. 18704. \
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= 0 for r > a (lb)
Pxeiu"
T7o = : 7- sin 0 for r < a z9 2-na(a2-r2)
= 0 for r > a (lc) (b) Uniform Contact Shear Distribution:
ffz =• 0 (2a)
Tzr = , cos 0 for r < a
= 0 for r > a (2b)
Pxe'-" TZ8
= r s i n i for r<a TTfl
= 0 for r > a (2c)
(c) Parabolic Contact Shear Distribution:
<rz = 0 (3a)
2Px(a2 - r2)eiwt
T2r = 2 c o s 9 f° r r < a
ir a = 0 for r > a (3b)
2Px(a2 - r V "
TZ6 = T sin0 for r<a TTfl
= 0 for r > a (3c)
in which a = the radius of area over which the load is assumed to be acting. Expressing the three types of contact shear distributions as a Fourier-Bessel integral (1) and substituting the boundary condition that the vertical stress CT2 due to horizontal load = zero (6,11), the displacement, U at any point (r, 0) on the surface (z = 0), in the direction of horizontal force Px is
U = u cos 0 + v sin 0 (4a)
f Px M(xa)\£K2 a lh(xr) in which u= Ji{xr)
J0 TxGa x \_F(x) Br p r
• e'°" cosQdx (4b)
f Px M(xa)\£k2h(xr) 1 d 1 M .
J0 uGa x \P{x) r p dr J
in which M(xa) = sin (xa)/2 for rigid base, = h(xa) for uniform and = 4]2(xa)/xa for parabolic contact shear distributions, respectively. F(x) = (2x2 - k2)2 - 4apx2, p = (x2 - h2)1'2, a = (x2 - k2)1'2, k = pw2/G, h2
= pco2/(^ + 2G), X = Lame's constant, G = shear modulus, and p = mass density of the semi-infinite solid.
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Displacement Conditions.—Using Eq. 4 the central displacement, Uc, is determined by putting r = 0, 6 = 0. The average displacement, Ua and the weighted average displacement, Uw are evaluated by the expressions
4 f r'2
!i„ = — U-rdr-dQ (5a) ir« Jo Jo
fa rir/2
and UW = A \ | p^U-rdr-dQ. (5b)
in which px = 1/2 in? (a2 - r2)1 / 2 for rigid base, = 1/TTA2 for uniform, and = 2(fl2 - r2)/irfl4 for parabolic contact shear distributions, respectively. By changing the order of integration, simplifying and substituting x = kn, a0 = ka, and h/k = s and simplifying, the displacements Uc, Ua and Uw are given by
Uc-Pxe'°" 2 _ -IN 1/2 (n2 - 1)
2-nGaJo I F(n) (n2 - 1) 1/2
u. = -P r e"
LT„ = :
luGa j 0
Pre"°'
1/2 (*' - 1)
F(n) (n2 - 1)1/2.
V - 1)1/2 1 2<i7GflJ0 [ F(n) ( n 2 - l ) 1 / 2 _
M(a0n)dn (6a)
2-M(a0n)-J1(a0n)
a0n
2-[M(a0n)]2
a0n
•dn
dn
(6b)
(6c)
in which F(n) = (2n2 - l ) 2 - 4n2(n2 - s2)1/2(n2 - 1)1/2, and nondi-
Reissner's method (8 ) Contour integration
Frequency f a c t o r , a 0
FIG. 1.—Comparison of fx and f2 Values Determined by Reissner's Method (10) and Contour Integration
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TABLE 1.—Values of bv lor Different Poisson's Ratios
M-(1)
0 1/4 1/3 1/2
s2
(2)
1/2 1/3 1/4
0
b0
(3)
- 2 - 7 / 4 - 5 / 3 - 3 / 2
bi
(4)
- 9 / 8 - 1 3 / 1 6 - 5 3 / 7 2 - 5 / 8
b2
(5)
- 6 7 / 6 4 -125/192 -1975/3456 - 1 5 / 3 2
mensional frequency factor, a0 = wa(p/G)1/2. A comparison (Fig. 1) of the displacement functions, /i and f2 evaluated for rigid base pressure distribution, weighted average displacement, by using Reissner's (8) method and by contour integration (1), for vertical vibration showed very good agreement. For reasons of simplicity, Reissner's (12) method has been adopted in this study, to evaluate the displacement functions, /] and f2. By splitting the integral and separating the real and imaginary parts, Eq. 6 can be expressed in the form
u = fa(h + ih) (7)
The displacement function, / i , can be expressed as a series function of nondimensional frequency factor, a0 in the form (12)
h 2 T T ^ 0
K-Gx 7
(8)
in which bv and Gv are constants. The values of bv and Gv for, = 0, 1 and 2 are evaluated and presented in Tables 1 and 2. The value of bv is
TABLE 2.—Value of G sure Distributions
Displacement condition
(1)
Central"
Average
Weighted average
„ for Different Displacement Conditions and Contact Pres-
Contact pressure distribution
(2)
Rigid base Uniform Parabolic Rigid base
Uniform
Parabolic
Rigid base
Uniform
Parabolic
Go (3)
TT/4
1 4/3 TT/4
8
3TT
128
45TT
IT/4 8
3TT
1,024
315ir
G1
(4)
- T T / 8
- 1 / 3 - 4 / 1 5
- 5 T T / 3 2
- 6 4 •
45TT
-2 ,048
1,575TT
- I T / 6
- 6 4
45TT
-16,384
14,175TT
G2
(5)
ir/96 1/45
4/315 7ir/256
1,024
4,725TT
16,384
99,225-rr TT/30
1,024
4,725TT
131,072
1,091,475TT
"Values of Gv for central displacement are taken from Sung (1953).
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TABLE 3.—Values of the Coefficients Xt, X2, X3
Conditions and Contact Shear Distributions
Displacement condition
d) Central
Average
Weighted average
Contact pressure distribution
(2)
Rigid base Uniform Parabolic
Rigid base Uniform Parabolic
Rigid base Uniform Parabolic
X1
(3)
1 1 1
1 1 1
1 1 1
for Different
X2
(4) -1 /6 -1 /8 -1/12
-7/24 -1 /4 -5/24
-1 /3 . - 1 /4 -1 /6
Displacement
x3 (5)
1/120 1/192 1/384
11/320 5/192 7/384
2/45 5/192 7/576
a function of Poisson's ratio only and the value of G„ is a function of type of contact shear distribution and displacement condition. On numerical integration, the displacement function, f2, can be expressed as
f2 = 0.113688(Xi^o - 0.064197(X2)ag + 0.046855(X3)a50 (9a)
f2 = 0.106076(X^flo - 0.059227(X2)a^ + 0.044019(X3)a^ (9b)
f2 = 0.102290(X1)tf0 - 0.057487(X2)«g + 0.043267(X3)a50 (9c)
f2 = 0.094542(X!)fl0 - 0.054933(X2)a3
0 + 0.042339(X3)a5
0 (9d)
•o c a
M = O . O u=0.25 11=0.33 11=0. 5
\ \ ^ - / l = 0
\ ^ / 1 = 0.
^ ' 2
) 25 33 5
0.5 1-0 1-5
Non d imens iona l frequency f a c t o r , d 0
FIG. 2.—Relationship Between Displacement Function fx, f2 and Frequency Factor, «„
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TABLE 4.—Values of Stiffness Coefficients for Horizontal Mode
Displacement condition
0)
Central
Average
Weighted average
Contact Shear Distribution
Rigid base (2)
8G«
2 - j i (Mindlin, 8)
8Gfl
2-M-(Mindlin, 8)
8Gfl 2 - |x
(Mindlin, 8)
Uniform (3)
2irG«
2 — |x (Authors)
3n2Gfl
4(2 - V ) (Authors)
3TT2G«
4(2 - n) (Authors)
Parabolic (4)
3TTG«
2(2 - p.) (Authors) 45TrzGfl
64(2 - v) (Authors) 315Tr2Ga
512(2 - M-) (Authors)
for four values of Poisson's ratio, u., viz., 0.00, 0.25, 0.33 and 0.50, respectively. The values of the constants Xi , X2 , X3 which are functions of the type of shear distribution and displacement condition are presented in Table 3. Fig. 2 presents the typical results of variation of displacement function ft, /2 with nondimensional frequency factor, a0 for weighted average displacement condition—uniform shear distribution. Similar results could be obtained for other cases of displacement and shear distribution conditions using Tables 1, 2 and 3 and Eqs. 8 and 9.
The value oifi for aQ = 0, represents the factor -Ga/K, where K is the static stiffness coefficient. Table 4 presents the values of K for three types of contact shear distribution and displacement conditions.
CONCLUSIONS
For the prediction of response of footings subjected to horizontal vibration, different types of contact shear distributions and displacement conditions are to be considered. Solutions using elastic half-space theory are not available for all the cases of shear distribution and displacement condition. In this paper, solutions have been obtained for the cases in which solutions are not available and the relevant coefficients have been presented in Tables which could be used in the appropriate equations for the prediction of dynamic response. Spring constants have been evaluated and tabulated for different displacement and shear distribution conditions.
APPENDIX.—REFERENCES
Bycroft, G. N., "Forced Vibration of a Rigid Circular Plate on a Semi-infinite Elastic Space or on an Elastic Stratum," Philosophical Transactions of the Royal Society, London, Series A, Vol. 248, No. 948, 1956, pp. 327-368. Chae, Y. S., Hall, J. R., Jr., and Richart, F. E., Jr., "Dynamic Pressure Distribution Beneath a Ring Footing," Proceedings, Sixth International Conference on Soil Mechanics and Foundation Engineering, Montreal, Canada, Vol. 2, 3/5, Sept., 1965, pp. 22-26. Gladwell, G. M., "Forced Tangential and Rotatory Vibration of a Rigid Cir-
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cular Disc on a Semi-infinite Solid/' International Journal of Engineering Science, Pergamon Press, Vol. 6, 1968, pp. 591-607.
4. Housner, G. W., and Castellani, A., "Discussion of Comparison of Footing Vibration with Theory," Journal of Soil Mechanics and Foundations Division, ASCE, Vol. 95, No. SMI, Proc. Paper 6324, Jan., 1969, pp. 360-364.
5. Hsieh, T. K., "Foundation Vibrations," Proceedings, Institution of Civil Engineers, London, Vol. 22, Paper No. 6571, June, 1962, pp. 211-226.
6. Luco, J. E., and Westmann, R. A., "Dynamic Response of Circular Footings," Journal of Engineering Mechanics Division, ASCE, Vol. 97, No. EMS, Proc. Paper 8416, Oct., 1971, pp. 1381-1395.
7. Moore, P. J., "Calculated and Observed Vibration Amplitudes," Journal of the Soil Mechanics and Foundations Division, ASCE, Vol. 97, No. SMI, Proc. Paper 7789, Jan., 1971, pp. 141-148.
8. Reissner, E., "Stationare, Axial Symmetriche durch eine Schittelnde masse erregte Schwingungen einess homogenen elastichen halbraumes," Ingen-ieur—Archiv., Vol. 7, Part 6, Dec, 1936, pp. 381-396.
9. Richart, F. E., Jr., and Whitman, R. V., "Comparison of Footing Vibration with Theory," Journal of Soil Mechanics and Foundations Division, ASCE, Vol. 93, No. SM6, Proc. Paper 5568, Nov., 1967, pp. 143-168.
10. Sezawa, K., "Further Studies on Rayleigh Waves Having Some Azimuthal Distribution," Bulletin, Earthquake Research Institute, Tokyo, Japan, Vol. 6, No. 2, 1929, pp. 1-18.
11. Veletsos, A. S., and Wei, Y. I., "Lateral and Rocking Vibration of Footings," Journal of Soil Mechanics and Foundation Division, ASCE, Vol. 97, No. SM9, Proc. Paper 8388, Sept., 1971, pp. 1227-1248.
MINIMUM SCF FOR TWO NEIGHBORING HOLES IN DISKS BY PHOTOELASTICITY
By N. K. Naik1 and K. Rajaiah2
INTRODUCTION
In engineering structures, openings of circular or other forms generally occur in groups. Their presence alters the stress distributions in their neighborhood invariably increasing the stress concentrations considerably. Examples of this kind are found in various engineering constructions and one of the earliest photoelastic investigations on this problem in ship structures is given in Ref. 5. Minimizing the stress concentrations in these structures is an important engineering problem.
'Lect., Aeronautical Engrg. Dept., I.I.T., Bombay-400 076, India. 2Prof., Aeronautical Engrg. Dept., I.I.T., Bombay-400 076, India. Note.—Discussion open until September 1, 1984. To extend the closing date
one month, a written request must be filed with the ASCE Manager of Technical and Professional Publications. The manuscript for this paper was submitted for review and possible publication on June 3, 1983. This paper is part of the Journal of Engineering Mechanics, Vol. 110, No. 4, April, 1984. ©ASCE, ISSN 0733-9399/ 84/0004-0654/$01.00. Paper No. 18704.
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