Abstract
Using the microstructural mechanics approach, the macroscopic anisotropic failure criteria expressed in closed form by the microscopic parameters are derived for regularly arranged elliptical particle assemblies. The close-packed, elliptical particle assembly is equivalent to a lattice model that is described by a lattice beam system, and the Mohr–Coulomb-like shear failure criterion is applied to describe the beam breakages. Through mechanical analysis of the instability state of the unit cell of the lattice beam system, macroscopic anisotropic strength criteria and the corresponding strength parameters, which are expressed by microscopic parameters and the tilting angle, are proposed. The macroscopic failure characteristics and strength parameters are qualitatively consistent with the results of the discrete element method (DEM), and the influences of the microscopic parameters and tilting angle on the macroscopic strength parameters are investigated in detail according to the proposed theoretical results. The applicability of the theoretical results to randomly distributed particles is explored by DEM simulation of irregularly arranged particles, and the deviation are also systematically discussed.
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Abbreviations
- \(a\), \(b\) :
-
Major and minor axes of the ellipse, respectively
- c b :
-
Microscopic shear resistance
- c :
-
Macroscopic cohesion
- e :
-
Void ratio
- f ih(i = n, s, m):
-
Internal force/moment at i direction of beam h at the middle section
- F sh :
-
Shear strength of beam h
- F x, F y :
-
External equivalent normal forces acting on the unit cells of lattice
- \(k_{i}^{h}\)(i = n, s, m):
-
Contact stiffness at i direction of beam h
- l h :
-
Length of beam h
- m :
-
Major–minor axis ratio of elliptical particles
- n :
-
Coordinate number
- R s :
-
Peak shear force of bond
- R t :
-
Peak tensile force of bond
- T xy (T yx):
-
External equivalent shear forces acting on the unit cells of lattice
- x i (i = n, s, m):
-
Relative displacement/rotation at i direction
- α :
-
Angle between the direction along beam 2 or 3 and the vertical direction
- γ :
-
Contact anisotropy ratio
- δ :
-
Tilting angle
- δ i (i = 0–4):
-
Critical tilting angle between different failure types
- λ :
-
Tangential–normal contact stiffness ratio
- μ b :
-
Microscopic friction coefficient of bond
- ξ :
-
Rolling–normal contact stiffness ratio
- σ x ′ (σ y ′):
-
Normal stress of the unit cell
- τ x ′ y ′ (τ y ′ x ′):
-
Shear stress of the unit cell
- φ :
-
Internal friction angle
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Acknowledgements
This study was supported by Major Program of National Natural Science Foundation of China (Grant No. 51890911), the National Natural Science Foundation of China (Grant Nos. 12272274, 11872281), the Hainan Province Science and Technology Special Fund (Grant No. ZDYF2021SHFZ264), the Fundamental Research Funds for the Central Universities (Grant No. 22120230302) and the State Key Laboratory of Disaster Reduction in Civil Engineering (Grant No. SLDRCE19-A-06). This support was greatly appreciated.
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Appendices
Appendix A
Figure A1 shows the force analysis of the unit cell in Fig. 2d, where F1, F2 and F3 are the redundant axial force, shear force and bending moment, respectively, of rigid beams 4 and 7. According to the symmetric characteristic of the unit, Fi (i = 1, 2 and 3) in beams 4 and 7 are equal.
\(\delta_{ij}\) and \(\Delta_{{i{\text{P}}}}\) represent the displacement in the Fi (= 1, 2 and 3) direction induced by the unit redundant force \(\overline{F}_{j} (j = {1, 2, 3})\) and external forces Fx, Fy and Txy. They can be calculated by the principle of virtual work as follows:
where \(k_{ih}\)(i = n, s, m) and lh are the contact stiffness along i direction and length of beam h, respectively; k is a parameter related to the shape of the cross section; and n = 9 represents the number of rigid beams. Additionally, \(\overline{F}_{{{\text{N}}i}}^{h}\), \(\overline{F}_{{{\text{S}}i}}^{h}\) and \(\overline{M}_{i}^{h}\) (\(F_{{{\text{NP}}}}^{h}\), \(F_{{{\text{SP}}}}^{h}\) and \(M_{{\text{P}}}^{h}\)) are the axial force, shear force and bending moment, respectively, of beam h induced by the unit redundant force \(\overline{F}_{i}\) (external forces Fx, Fy and Txy) of the rigid beam (beams 4 and 7) force. Note that to keep consistent with the theoretical derivation, the material constants of original principle of virtual work [24] are replaced by contact stiffesses \(k_{i}\) in this study according to the relations between material constants and contact stiffesses [3]. According to the typical equations of the force method in structure mechanics, \(\delta_{ij} F_{i} + \Delta_{ip} = 0\), the redundant force Fi of rigid beams 4 and 7 can be expressed as:
where
Substituting Eq. (1) and the lengths of beams in Table 1 into Eqs. (A-4) and (A-6), we obtain the dimensionless strength coefficients shown in Eqs. (13–15). After the redundant force of rigid beams 4 and 7 is determined, the internal forces of all remaining beams can be obtained in Eqs. (10–12) by force analysis of the statically determinate structure.
Appendix B
O, P, Q in Eq. (29) can be expressed as:
where ai, bi, ci and di (i = 1, 2) for δij can be expressed as:
δ12: \(a_{1} = 2mB\), \(a_{2} = \left[ {\left( {\frac{1}{2} - \sqrt 3 mB} \right) - \mu_{p} \left( {B + \frac{\sqrt 3 m}{2}} \right)} \right]\), \(b_{1} = 0\), \(b_{2} = - \frac{\sqrt 3 }{m}\left[ {C + \frac{{m^{2} }}{2} + \sqrt 3 m\mu_{p} \left( {\frac{1}{6} - E} \right)} \right]\),
\(c_{1} = \sqrt 3 (2A - 1)\), \(c_{2} = - A\left( {3 + \frac{{\sqrt 3 \mu_{p} }}{m}} \right)\), \(d_{1} = - mR_{t} /a\), \(d_{2} = - \sqrt {3m^{2} + 1} c_{p} /a\);
δ23: \(a_{1} = \left[ {\left( {\frac{1}{2} - \sqrt 3 mB} \right) - \mu_{p} \left( {B + \frac{\sqrt 3 m}{2}} \right)} \right]\), \(a_{2} = \left( {B + \frac{\sqrt 3 m}{2}} \right)\), \(b_{1} = - \frac{\sqrt 3 }{m}\left[ {C + \frac{{m^{2} }}{2} + \sqrt 3 m\mu_{p} \left( {\frac{1}{6} - C} \right)} \right]\), \(b_{2} = 3\left( {\frac{1}{6} - C} \right)\), \(c_{1} = - A\left( {3 + \frac{{\sqrt 3 \mu_{p} }}{m}} \right)\), \(c_{2} = \frac{\sqrt 3 A}{m}\) \(d_{1} = - \sqrt {3m^{2} + 1} c_{p} /a\), \(d_{2} = \sqrt {3m^{2} + 1} R_{t} /a\);
δ-23: \(a_{1} = \left[ {\left( {\frac{1}{2} - \sqrt 3 mB} \right){ + }\mu_{p} \left( {B + \frac{\sqrt 3 m}{2}} \right)} \right]\), \(a_{2} = \left( {B + \frac{\sqrt 3 m}{2}} \right)\), \(b_{1} = - \frac{\sqrt 3 }{m}\left[ {C + \frac{{m^{2} }}{2} - \sqrt 3 m\mu_{p} \left( {\frac{1}{6} - C} \right)} \right]\), \(b_{2} = 3\left( {\frac{1}{6} - C} \right)\), \(c_{1} = - A\left( {3 - \frac{{\sqrt 3 \mu_{p} }}{m}} \right)\), \(c_{2} = \frac{\sqrt 3 A}{m}\) \(d_{1} = \sqrt {3m^{2} + 1} c_{p} /a\), \(d_{2} = \sqrt {3m^{2} + 1} R_{t} /a\);
δ34: \(a_{1} = \left[ {\left( {\sqrt 3 Bm - \frac{1}{2}} \right) - \mu_{p} \left( {B + \frac{\sqrt 3 m}{2}} \right)} \right]\), \(a_{2} = \left( {B + \frac{\sqrt 3 m}{2}} \right)\), \(b_{1} = - \frac{\sqrt 3 }{m}\left[ {C + \frac{{m^{2} }}{2} + \sqrt 3 m\mu_{p} \left( {C - \frac{1}{6}} \right)} \right]\), \(b_{2} = 3\left( {\frac{1}{6} - C} \right)\), \(c_{1} = A\left( {3 - \frac{{\sqrt 3 \mu_{p} }}{m}} \right)\), \(c_{2} = \frac{\sqrt 3 A}{m}\) \(d_{1} = - \sqrt {3m^{2} + 1} c_{p} /a\), \(d_{2} = \sqrt {3m^{2} + 1} R_{t} /a\);
δ24: \(a_{1} = \left[ {\left( {\frac{1}{2} - \sqrt 3 mB} \right) - \mu_{p} \left( {B + \frac{\sqrt 3 m}{2}} \right)} \right]\), \(a_{2} = \left[ {\left( {\sqrt 3 Bm - \frac{1}{2}} \right) - \mu_{p} \left( {B + \frac{\sqrt 3 m}{2}} \right)} \right]\), \(c_{1} = - A\left( {3 + \frac{{\sqrt 3 \mu_{p} }}{m}} \right)\).
\(b_{1} = b_{2} = - \frac{\sqrt 3 }{m}\left[ {C + \frac{{m^{2} }}{2} + \sqrt 3 m\mu_{p} \left( {\frac{1}{6} - C} \right)} \right]\), \(c_{2} = A\left( {3 - \frac{{\sqrt 3 \mu_{p} }}{m}} \right)\), \(d_{1} = d_{2} = - \sqrt {3m^{2} + 1} c_{p} /a\).
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Zhou, Z., Wang, H. & Jiang, M. Micromechanical mechanism-based anisotropic strength criteria for regularly arranged elliptical particle assembly. Acta Geotech. (2023). https://doi.org/10.1007/s11440-023-02109-7
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DOI: https://doi.org/10.1007/s11440-023-02109-7