By Shireen Afshan, Daniel Balint, Jianguo Lin (auth.), Holm Altenbach, Serge Kruch (eds.)
This quantity provides the most important consequence of the IUTAM symposium on “Advanced fabrics Modeling for Structures”. It discusses advances in extreme temperature fabrics study, and likewise to presents a dialogue the hot horizon of this primary box of utilized mechanics. the themes conceal a wide area of analysis yet position a selected emphasis on multiscale methods at numerous size scales utilized to non linear and heterogeneous fabrics.
Discussions of latest ways are emphasized from a variety of comparable disciplines, together with steel physics, micromechanics, mathematical and computational mechanics.
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Altenbach and Y. 5 mm Fig. 1 Failure of the steel AISI type 316 components at Eddystone unit no. 1 power station, after  weld failures, erosion, etc. Thus, failure occurs due to the complex interaction of creep deformation mechanisms and other material behavior processes, which lead to an acceleration of the material degradation. Therefore, for the purpose of correct simulation of a creep failure case study (CFCS), appropriate life time assessment and precise prediction of failure location, it is necessary to apply unified material behavior models.
The elastic strain εel is characterized by the temperature dependent Young’s modulus E. A portion of εpl is defined by the hardening processes, which induce the evolution of both hardening parameters—relatively slow saturating isotropic H and relatively fast saturating kinematic K . e. at high stresses mainly by H and at low stresses mainly by K . The time-dependent inelastic response is the slow increase of the creep strain εcr with a variable creep strain rate ε˙ cr . Depending on the character of creep strain acceleration ε¨ cr , three stages can be considered in a typical creep curve as illustrated in Fig.
For the sake of simplicity, we restrict ourselves to an isotropic material. We also assume that the bulk material is elastic but the surface stresses are viscoelastic. Hence, we have the Hooke law for the bulk material σ = 2με + λItr ε with ε = ε(u) ≡ 1 ∇u + (∇u)T , 2 (3) where ε is the strain tensor, λ and μ are Lamé’s moduli, and I is the three-dimensional unit tensor, respectively. For the surface stresses we assume the following constitutive equation t τ =2 −∞ t μ S (t − τ )˙e(τ ) dτ + λ S (t − τ )tr e˙ (τ ) dτ A, (4) −∞ 1 e = e(v) ≡ ∇ S v · A + A · (∇ S v)T , 2 where e is the surface strain tensor, v the displacement of the surface point x of Ω2 , A ≡ I − n ⊗ n the two-dimensional unit tensors, the overdot denotes differentiation with respect to time t, and λ S and μ S are the relaxation functions of the surface film Ω2 , respectively.
Advanced Materials Modelling for Structures by Shireen Afshan, Daniel Balint, Jianguo Lin (auth.), Holm Altenbach, Serge Kruch (eds.)