# MANY previous investigators have studied the elasticstress

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2 110 y JOURNAL OF APPLED MECHANCS CT.p(r, t/;) = 4 r 1 11t { a1 [ -3 cos ; - cos 3 : J + b1 [ -3 sin ; - 3 sin 3 : J} (a) FG. 1 GEOMETRY ( b) FORKED CRACK + 4a sin if; + O(r 1 h) +... [1] r,y,(r, t/;) = 4 r~f { a1 [-sin ; - sin 3 : J + b1 [cos ; + 3 cos 3 : J} function x(r, i/;) can be split into its even x.(r, t/;) and odd Xo(r, tf;) parts withrespect to if; (Fig. 1).x.(r, t/;) = :::: (-l)n- 1 a,,-1 r { n = 1,, 3,... [-cos ( n - n+_!_ f) if; + :: + ~ cos ( n + i) t/] + (-l)nanrn+ [-cos ( n -% ) if;+ cos ( n +})if;]}. [8] Xo(r, t/;) L:: {(-l)n- 1 bn-1r n + ~ n = 1,., 3,... + (-l)nb,,rn+i [-sin ( n - %) if; + ~: + ~ sin ( n + } ) if; J}... [9] t should be observed that even though the field equation and the boundary conditions along the radial edges are satisfied, the constants ai and bi are undetermined. Their values of course depend upon the loading conditions; more specifically, either upon the boundary conditions at infinity in the case of an infinite sector, or upon those at some fixed radius when the plate has finite dimensions. For the latter practical case, which includes the problem under consideration, all the higher eigenfunctions in general will be present in order to determine a solution in the large. Upon writing out the first few terms 3 [ ( x(r, if;) = r h if; 1 3tf;) a1 -cos - 3 cos + b1 (-sin ; - sin 3 :) J + ar [l - cos tf;j + O(r 6 h) +... [10] from which the associated stresses may be found from Equations (4-6] as {a1 [-5cos1_ +cos 3 t/j CT,(r, t/;) = - 1 4r 1 f. + b [ 5. if;. 3 1 t/]} - sm + 3sm + 4a cos if; + O(r 1 h) +... (11] -a sin tf; + O(r 1 l ) +... [13] Before proceeding further, it is convenient to identify the stress state which is multiplied by the constant a, viz. n the Cartesian co-ordinates analog of Equations (4-6], the stresses are CT., = 4a, CT 11 = O, and r "'' = 0 For most cases of interest, including the usual tension and bending specimens, CT,, along the edge x = -xo (see Fig. 1) is zero; hence for these cases CT,, = 4a = 0 and thus Equations [11-13] with respect to the radial variation are all of the form r-'/z + O(r'li), and the local stress variations in the vicinity of the base of. the crack, r--+- 0, are proportional, up to vanishing terms in r, to the contribution of the first term. f the boundary x = -x 11 were loaded, however, say by a uniform pressure, this contribution would have to be superimposed. t is convenient at this point to compute two quantities useful in photoelastic analysis; specifically, the sum of the normal stresses, which is proportional to the isopachic lines, and the difference of the principal stresses, which is proportional to the isochromatic lines. Thus 4 r~ls {a1 [-8 cos ; ] + b1 [ -8 sin ; J} +... CT1 + CT... (14) CT1 - CT = [(CT, - CT.p) + 4r,y,J1h ±1 { ( 3 )} 1 / 4 r'ls l6a1 sin if; + 64b1 - sin if; _ (15] The direction of principal stress is found from the condition that the shear stress, r n 81 on a plane whose normal is inclined at an angle a to the radius vector vanishes Tns = r,y, cos a - (1/)(CT, - CT.p) sin a = 0 O = -r- 1 / {[sin.t cos ; cos a - cos ; sin ; sin a J a1 + [cos ; ( - 3 cos ; ) cos a + sin ; ( - 3 sin ; ) sin a J b1} +... (16] The angle {j of a stress trajectory with the x-axis, Fig. 1, is then {j = i/t + a. Also the total strain-energy density

3 MARCH, cry,(r, 1/;) = ~ [-3 cos}! - cos 3 1/1] a, +... [4] 4r and the strain energy due to distortion alone, i.e., the total strain energy less that due to change in volume 1 = 1 G (3Toct)... [18] where the expression is given in terms of principal stresses (cr3 = 0 in this case), and the definition of the octahedral sh~aring stress has been used, may be written, respectively, as 3ErW = a 1 [ (34-30v) cos t + (1 + v) sin t + (1 + v) - 4(1 + v) cos 1/; J + b1 [ (34-30v) sin t + (1 + v) cos ~ + 18(1 + v) + 1(1 + v) cos 1/; J + a1b1 [ (3 - v) sin t cos t 6GrWd = a 1 (1+3 sin t) cos - 8(1 + v) sin 1/; J [19] + b1 [ 3 + ( cos ~ ) ( 1-3 cos ~ ) sin t J t + a1b1 sin 1/; [0] n the foregoing expressions it is seen that the term multiplied by the coefficient a1b 1 represents a coupling between the symmetric and antisymmetric variations with respect to 1/;. Finally, the displacements (see reference 7) are found to be { [( µu,(r, 1/;) = r h a cr ) cos 1/; 1 31/;J + cos Tr.p(r, 1/;) = ---; [. 1/;. 31/;J 4r 1 µur(r, 1/;) = r'h [ (-t + 4cr) cos t -sm - - sm - a [5] + ~ cos 3 t J a, +... [61 µuy,(r, 1/;) = r'h [ ( f - 4cr) sin ~ - f sin 3 t J a [7] CT1 + CT = ~/ [-8cos1.J n r -4-1 [4a1 sin if;] r... [8]... [9] f3n-i = (31/;/4) ± (7r/4); also isotropic locus at if; ~ 0.. [30] W = ~ cos j;_ [1 - v + (1 + v) sin i...j +... [311 Er t is observed that, for this elastic behavior in an isotropic homogeneous material, the stress system represented by the first term possesses the characteristic square-root singularity found by nglis (1), Westergaard (4), and others; also, the shapes of _the isopachics and isochromatic fringes are in agreement with photoelastic data obtained by Post (6) and corroborated independently at GALCT. n addition, however, there are certain other interesting features which, because of the relative simplicity of the previous expressions, become readily apparent. + b 1 [ (-3 + 4cr) sin ; +sin 3 t]} +... {1],/, '/ 1 µu y,(r,.,,) = r { [( 7 ).. 1/; 1. 31/;J a1-4cr sm - sm CRACK CRACK + b1 [ - ( f - 4cr) cos t + ~ cos 3 t J} +... [] where cr=v/(l+v) SYMMETRCAL STRESS D1sTRBUTON For the sake of simplicity it is convenient to analyze the two types of solutions separately; the symmetric solutions, i.e., b, = 0, are perhaps the more common, occurring, for example, in the case of an edge crack in a thin plate subjected to bending or tension. Specializing the stresses and the other quantities to this case gives 1 [ 1/; 31/;J cr,(r, 1/;) = 4 r 1 h -5 cos + cos a [3] (o) SYMMETRC CASE n-;' 1 sin o/ Frn. (b) ANTSYMMETRC CASE "/ r. 3 Jl/ n~r ~-4 sin y sochromatc-frnge PATTERNS The first of these relates to the observation that the shear stress is zero along the line of propagation of the crack (1/; = 0). The er, and cry, stresses must therefore be principal stresses as expected, but moreover from Equation [9] the stresses are equal CT1 (0) - CT(0) = (-a 1)r- 1 h +... n other words, at the base of the crack there exists a strong tend-

4 11 JOURNAL OF APPLED MECHANCS er eo"' (o) SYMMETRC CASE "' 180 (o) Symmetric a 0.5 Oj (1+u) b 1. e wd (0) = Er FG. 3 ( b) ANTSYMMETRC CASE PRNCPAL-STRESS VARATONS ency toward a state of (two-dimensional) hydrostatic tension which consequently may permit the elastic analysis to apply closer to the point of the crack that was hitherto supposed, notwithstanding.the square-root stress 8ingularity. n order to investigate this point a bit more fully, particularly for the hig~er terms in r, i.e., further away from the crack point, more terms can be considered in Equations (3] and [4] to obtain, for t/; = 0 u,(r, 0) : n=l,, (-l)n(n - )an-it n - Z.. (33] uy,(r, 0) _ : {c-l)n(n - )an-1/ - ~ n - 1, (-1r+ 1 a,jn - l)rn-1}... [34] from which it may be concluded that, if the constant loading term a = O, the principal stresses are equal up to the linear term in r. From the previous relation the difference between the stresses can then be written u, - uy, L: (-1)"a,.(n - l)rn- 1. [35].n = 1,, 3... Therefore the principal stresses will become progressively unequal and the tendency toward hydrostatic tension reduced as the distance from the crack increases. As a matter of interest the stress trajectories for the lowest eigensolution, n = 1, are shown in Fig. 5 and they are observed to be of the interlocking type which explains the apparent contraction that fj = ±?r /4 for t/; = 0 from Frn (b) Antisymmetric STRAN-ENERGY-DENSTY DSTRBUTONS Equation (30]. The equality of the principal stresses leads to a locus of isotropic points. Another interesting characteristic of the solution is shown in Fig. 4 which shows the variation of distortion strain energy as a function of angle for a fixed radius. B.ecause of the afore-mentioned hydrostatic tendency, the maximum energy of distortion does not occur along the line of crack direction, but rather at t/;* = ±cos- 1 (1/3) "" ±70 deg where it is one third higher. The previous results also give the principal stress as a, t/; [. t/; J <1'1. = - ~/. COS - 1 =F Sill - r ' for which the maximum value of (3v3/4)(-a 1 )r-'1 1 occurs at "j, = cos- 1 (1/) = 11" /3 at which angle the stress trajectories are parallel to the x, y-co-ordinates; i.e., fj = 0, 7r/. The maximum shear stress Tmax = 1/ (u1 - u) oriented at fj = 7r /8, 5w/8, t/; = 11" / and equals exactly one half the hydrostatic tension value to which the normal stresses are subjected along t/; = 0 at the same radial distance. Some of the foregoing properties are summarized in Fig. 6. Finally, the radial and circumferential displacements on the free edges from Equations [3] and [4] are found to be zero and ±4(1 + v)- 1 a,r 1 l, thus leading to the expected fact that the two faces will have closed together and overlapped under a compression loading, an impossible situation by itself requiring a 1 = 0. "'

5 MARCH, O'"o / /,,,.,, /~, 0,,.,,.,,.,,,.- Q1CTo /' 60 MoK. Tensile Stress FJG. 5 STRESS TRAJECTORES FOR LOWEST EVEN EGENFUNCTON fj = (3f /4) ± ('f /4) n this case one is led to the contact problem treated by Westergaard (4) wherein there is no stress singularity at the point of the crack. ANTSYMMETRCAL STRESS DSTRBUTON When the stress distribution is antisymmetric, which is a case that does not seem previously to have been treated explicitly, such as may exist about a crack parallel to the neutral axis of a beam in pure bending, there results u (r '') = _!_ [-5 sin ± + 3 sin~] b [36] r ' 'Y 4r1 t <Tf(r, 1/;) = ~ [-3 sin.i_ - 3 sin 3 1f] b [37] 4r T,f(r, if;) = 4 r~; 1 [cos ~ + 3 cos 3 : J b [38] µu,(r, if> = r 1 [ (-3 + 4u) sin + µv f(r, 1/;) = r 1 f 1 [ - ( ~ - 4u )cos ~ +sin ~f J b [39] + f cos 3 : J b [40] <T1 + u =~ [-8 sin±] b [-HJ 4r <11 - <1 = 4 r~/t [ 8 ( 1 -! sin 1/; } 1 '] b [4] W = ~ [<1 - v) sin ± + (1 + v) Er b1 [1 + v. if d Er 3 W = - --sm - + (1 + v) ( 1 - ~ sin 1/;) J +... [43] ( 1 - ~ sin lf') J +... [44] FG. 6 CRTCAL PRNCPAL STRESSES FOR THE LOWEST EVEN EGENFUNCTON TO = -a1ro- 1 /1 Again in this case the singular stress system varies as r- 1 / 1 ; the distortion-strain-energy-density variation is shown in Fig. 4. t is interesting to observe that in this case the energy drops on either side from a relative maximum in the direction of the crack to a minimum of 40 per cent of its if = 0 value at f* = cos- 1 (1/9). t would be interesting to experiment photoelastically with the antisymmetric-loading condition, which is not too simple a matter, in an analysis similar to that of Post for the symmetrical case. CONCLUSON While it is not the intent to extend the range of validity of the elastic analysis by delving into the complicated phenomenon of failure or fracture mechanics, it does seem pertinent to remark upon some possible implications of the results obtained from elasticity theory. First of all it seems that even in the presence of a partial (twodimensional) hydrostatfo-stress field there would be a reduced tendency for yieldin11; at the base of the crack. Then, as the magnitude of the individual stresses increases as the inverse half power of the radius, the stress should become quite high with a tendency toward a cleavage failure. At the same time the elastic analysis indicates there should be a large amount of distortion off to the sides of the crack and presumably some yielding should take place in these areas which would tend toward a ductile failure. The character of failure actually occurring in a given specimen would depend upon the material. n this connection it is pertinent to mention some recent experimental evidence of Forsyth and Stubbington (8) called to the author's attention by S. R. Valluri, which tends to substantiate the remarks concerning an area of yielding off the crack direction, presumably ±70 deg for an exactly symmetrical loading. n addition, because the stress becomes nonhydrostatic as the distance from the point of the crack increases, by Equation [35]. there may be reason therefore to suspect a yielded region ahead of the crack also, although not as severe. As a second remark, concerning the direction of cracking or forking, it is recognized that slow-moving cracks generally propagate more or less straight. 4 Because some cracks do fork, 'n an interesting piece of work Yoffe (9) has discussed the chitnge of direction of a running crack due to its velocity and has found that if the material is such that a crack propagates in a direction normal to the maximum tensile stress (which, incidentally, is not uf as she apparently has assumed; indeed aside from the principal stresses, ur ;::: 111f), there is a critical velocity of about 0.6 times the velocity of shear waves in the material above which the crack tends to become curved. t may be of value to supplement her work by testing her hypothesis with respect to the maximum principal tensile stress; it is suspected, however, that the results will be qualitatively the same because, as she has remarked and as is shown in Fig. 6, the stress field is relatively uniform over a wide area in front of the crack.

6 114 however, it may be worth noting that any arbitrary crack will be subjected simultaneously to both symmetric and antisymmetric loading. n this connection it is observed that for the antisymmetric contributions the relative maximum and minimum energies, for example, tend to negate the effects which occur for a symmetrical loading. One might therefore conclude that for randomly oriented cracks there would be no preferred direction that the crack might take upon moving, with macroscopic structure and rate-of-energy release being controlling factors. On the other hand, it may be possible to relate the maximum principal tensile stresses occurring at ±60 deg, in the neighborhood of the maximum distortion, to the angle crack-forking phenomenon shown, for example, by Post (6) or in Fig. l(b), although again for metals as opposed to plastics the effect of crystal orientation and slip planes probably would be quite strong. BBLOGRAPHY "Stresses in a Plate Due to the Presence of Cracks and Sharp Corners," by C. E. nglis, Transactions of the nstitution of Naval Architects, London, England, vol. 60, 1913, p. 19. JOURNAL OF APPLED MECHANCS "The Phenomena of Rupture and Flow in Solids," by A. A. Griffith, Philosophical Transactions of the Royal Society of London, England, vol. 1, 191, pp "Stresses at a Crack, Size of the Crack and the Bending of Reinforced Concrete," by H. M. Westergaard, Proceedings of the American Concrete nstitute, vol. 30, 1934, pp "Bearing Pressures and Cracks," by H. M. Westergaard, JOURNAL OF APPLED MECHANCS, Trans. ASME, vol. 61, 1939, pp. A "Experimental Study of Stresses at a Crack in a Compression Member," by S. C. Hollister, Proceedings of the American Concrete nstitute, vol. 30, 1934, pp "Photoelastic Stress Analysis for an Edge Crack in a Tensile Field," by D. Post, Proceedings of the Society for Experimental Stress Analysis, vol. 1, no. l, 1954, p "Stress Singularities Resulting From Various Boundary Conditions in Angular Corners of Plates in Extension," by M. L. Williams, JOURNAL OF APPLED MECHANCS, Trans. ASME, vol. 74, 195, p "The Slip Band Extrusion Effect Observed in Some Aluminum Alloys Subjected to Cyclic Stresses," by P. J.E. Forsyth and C. A. Stubbington, Royal Aircraft Establishment, MET Report 78, January, "The Moving Griffith Crack," by E. H. Yoffe, Philosophical Magazine, vol. 4, part, 1951, pp

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