Residual Strength and Fatigue Lifetime of ... - Solid Mechanics
Residual Strength and Fatigue Lifetime of ... - Solid Mechanics Residual Strength and Fatigue Lifetime of ... - Solid Mechanics
arising due to the junction between the insert and the core and to a slight unintentional mismatch between the core and the insert thicknesses, see Hayman et al. (2007). The intact panels with PMI core failed by a combination of shear crimping and global buckling, see Figures 3.14 (b) and 3.14 (c). Figure 3.15 shows the debond propagation load vs. the debond diameter, in each case the mean result for two or three specimen replicates is used. It appears that the debond propagation load decreases significantly with increasing debond diameter. Face sheet compression failure Figure 3.14: (a) Compression failure of a face sheet in an intact panel with H130 core (b) global bucking and (c) shear crimping of intact PMI panels. Failure load (kN) 500 400 300 200 100 0 (a) Global buckling 0 50 100 150 200 250 300 Debond Diameter (mm) 3.15: Measured propagation load vs. debond diameter. Measured failure loads for the intact panels can be identified for a debond diameter of 0 mm. The theoretical compressive failure loads for the intact panels, based on the material compressive strengths in Table 3.1, are shown in Table 3.4 together with the measured values. This table also shows the load at which wrinkling of the face sheets and shear crimping is predicted for each case. Wrinkling load of the face sheets is determined based on a formula proposed by Hoff et al. (1945): 52 (b) H130 H250 PMI Shear crimping (c)
(3.15) cr 0. 5 3 E f EcGc where Ef and Ec are modulus of elasticity of the face sheets and core and Gc is the shear modulus of the core. It is seen that wrinkling is likely to have influenced the strength of the A panels and both wrinkling and crimping are likely to have influenced the strength of the C panels. The observed behaviour raises an important question concerning the value of intact strength that should be used in determining a local strength reduction factor Rl. Should this be based on the compressive strength of a laminate measured in tests on small laminate samples in which all types of buckling are prevented, or should it be based on the compressive strength actually observed for the tested panel? Most types of buckling are dependent on the size of the panel and its boundary conditions. Moreover, they are not affected by very local losses of stiffness. Thus, it seems appropriate to base Rl on the basic compressive strength of the laminate and rather perform separate checks of possible effects of buckling. An exception to this is local wrinkling of the face sheet, which is independent of panel size and boundary conditions and in practice may provide a modified material strength to replace the value measured in tests on small laminate samples. 3.5: Measured and theoretical failure loads for intact panels. Lay-up Measured failure Theoretical failure loads (kN) type load (kN) Compressive failure Shear crimping Face sheet wrinkling A 325 448 642 409 B 357 502 1335 663 C 279 636 243 229 3.5 Panel Analysis A 3D finite element model was developed in the commercial finite element code, ANSYS version 11, using 8-node isoparametric elements (SOLID45). Geometrically non-linear analysis of the debonded panels was performed with displacement controlled loading. The panels were assumed to contain an initial imperfection in the form of a half-sinusoidal wave as determined from eigenbuckling mode shapes. The magnitude of the initial imperfection is obtained from DIC measurement of the test specimens shown in Figure 3.11. Because of geometry and loading symmetry only a quarter of the panel was modelled. Symmetry boundary conditions were applied to the symmetry planes. Due to the need for a high mesh density at the crack tip when performing the fracture mechanics analysis, a submodelling technique was employed. The finite element model and submodel are shown in Figure 3.16. 53
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arising due to the junction between the insert <strong>and</strong> the core <strong>and</strong> to a slight unintentional mismatch<br />
between the core <strong>and</strong> the insert thicknesses, see Hayman et al. (2007). The intact panels with<br />
PMI core failed by a combination <strong>of</strong> shear crimping <strong>and</strong> global buckling, see Figures 3.14 (b)<br />
<strong>and</strong> 3.14 (c). Figure 3.15 shows the debond propagation load vs. the debond diameter, in each<br />
case the mean result for two or three specimen replicates is used. It appears that the debond<br />
propagation load decreases significantly with increasing debond diameter.<br />
Face sheet compression<br />
failure<br />
Figure 3.14: (a) Compression failure <strong>of</strong> a face sheet in an intact panel with H130 core (b)<br />
global bucking <strong>and</strong> (c) shear crimping <strong>of</strong> intact PMI panels.<br />
Failure load (kN)<br />
500<br />
400<br />
300<br />
200<br />
100<br />
0<br />
(a)<br />
Global buckling<br />
0 50 100 150 200 250 300<br />
Debond Diameter (mm)<br />
3.15: Measured propagation load vs. debond diameter. Measured failure loads for the intact<br />
panels can be identified for a debond diameter <strong>of</strong> 0 mm.<br />
The theoretical compressive failure loads for the intact panels, based on the material compressive<br />
strengths in Table 3.1, are shown in Table 3.4 together with the measured values. This table also<br />
shows the load at which wrinkling <strong>of</strong> the face sheets <strong>and</strong> shear crimping is predicted for each<br />
case. Wrinkling load <strong>of</strong> the face sheets is determined based on a formula proposed by H<strong>of</strong>f et al.<br />
(1945):<br />
52<br />
(b)<br />
H130<br />
H250<br />
PMI<br />
Shear crimping<br />
(c)