Discussion of the Griffith fracture criterion in piezoelectricity
Transcrição
Discussion of the Griffith fracture criterion in piezoelectricity
Page 1 Workshop: Direct and Inverse Problems in Piezoelectricity Linz, October 06-07, 2005 Discussion of the Griffith fracture criterion in piezoelectricity Anna-Margarete Sändig [email protected] Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Outline 1. Introduction 2. The Griffith fracture criterion 3. 3D-Field equations 4. 2D-Field equations 5. Griffith formula 6. J-integral 7. Stress intensity factors 8. Conclusion Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Page 2 Introduction Page 3 The fracture behaviour in piezoelectric materials under mechanical and electrical loading is not fully understood. In particular, it is not clear, whether the electric field impedes or enhances crack propagation. Different fracture criterions for linear models are discussed in the literature: • Total energy release rate. (Pak 90) • Mechanical strain energy release rate. (Park/Sun 95) • Stress intensity factors. (Suo/Kuo/Barnett/Willis 92) • Local energy release rate. (Gao et al. 97) Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Introduction Page 3 The fracture behaviour in piezoelectric materials under mechanical and electrical loading is not fully understood. In particular, it is not clear, whether the electric field impedes or enhances crack propagation. Different fracture criterions for linear models are discussed in the literature: • Total energy release rate. (Pak 90) • Mechanical strain energy release rate. (Park/Sun 95) • Stress intensity factors. (Suo/Kuo/Barnett/Willis 92) • Local energy release rate. (Gao et al. 97) We will discuss the Griffith energy criterion which is based on the total energy release rate, in particular: • What is the total energy? • Which formulas for the energy release rate are available? • How are the Maz’ya-Plamenevski coefficient formulas related to the stress intensity factors? Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Griffith fracture criterion The Griffith criterion is based on energy balance: The body is in an equilibrium state, if the total energy is minimal, that means, the crack grows if there is a neighboured configuration with smaller energy as the actual configuration. g δ f Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Page 4 Griffith fracture criterion Page 4 The Griffith criterion is based on energy balance: The body is in an equilibrium state, if the total energy is minimal, that means, the crack grows if there is a neighboured configuration with smaller energy as the actual configuration. g δ f Total energy: Π = Û + D̂ = Ê − F + D̂ Û - potential energy, D̂- dissipative energy, Ê- elasto-electrical energy (electric enthalpy), R R 1 Ê = 2 AB(U ) · B(U ) dy − Ω M B(U ) · (−∇ϕ), Ω R R F- external energy, F = f U dy + gU da, Ω Field equations: −B > ABU = f in Ω, U = 0 on Γ, ABU = (σ, D)> = 0 on Γ± , g = 0. M B(U ) = D ΓN U = (u1 , u2 , u3 , ϕ)> Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation 3D Field equations Hooke’s law in 3D: P3 (C) γ − ijkl Ckl k,l=1 k=1 ekij (E)k , P P (D)i = 3j=1 (ε)ij (E)j + 3j,k=1 eijk (γ)jk (σ)ij = P3 Voigt’s notation: ! ! γ σ =A = AB D E Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Page 5 u ϕ ! , 3D Field equations Voigt’s notation: ! ! γ σ =A = AB D E Hooke’s law in 3D: P3 (C) γ − ijkl Ckl k,l=1 k=1 ekij (E)k , P P (D)i = 3j=1 (ε)ij (E)j + 3j,k=1 eijk (γ)jk (σ)ij = Page 5 P3 transversal isotrop, poling in y3 -direction A = 0 ∂1 B Div = @ 0 0 C e 0 ∂2 0 −e ε 0 0 ∂3 > ! 0 ∂3 ∂2 = c12 c13 0 0 0 0 0 −e31 c12 c11 c13 0 0 0 0 0 −e31 c c c 0 0 0 0 0 −e33 B 13 13 33 0 0 −e15 0 B 0 0 0 c44 0 B 0 0 0 0 c44 “ 0 ” −e15 0 0 B 12 0 0 0 B 0 0 0 0 0 c11 −c 2 0 c11 @ ∂3 0 ∂1 0 0 0 0 0 e15 e15 0 e31 e31 e33 0 0 1 ∂2 C ∂1 A , 0 0 0 B = 0 0 0 ε11 0 0 Div 0 > 0 ε11 0 0 0 ε33 ! 0 . −∇ 3D field equations: −B > A B U = f . Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation 1 C C C C, C A u ϕ ! , 2D Field equations Page 6 Reduction to 2D-Problems: U = U (x1 , x3 ) =⇒ Decoupling of the 3D-problem into a plane strain-state problem for (u 1 , u3 , ϕ) and anti-plane strain-state problem for u2 . Hookes law for the in-plane state (γ21 = γ22 = γ23 = 0, E2 = 0, U = (u1 , u3 , ϕ)> ): 1 0 σ11 c11 Bσ33 C Bc13 B C B B C B Bσ13 C = B 0 B C B @ D1 A @ 0 e31 D3 0 c13 c33 0 0 e33 0 0 c44 e15 0 0 0 −e15 ε11 0 10 −e31 ∂1 B −e33 C CB 0 CB 0 C B ∂3 CB 0 A@ 0 ε33 0 0 ∂3 ∂1 0 0 1 0 0 1 C 0 C u1 CB C 0 C @u3 A = ABU. C −∂1 A ϕ −∂3 Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation 2D Field equations Page 6 Reduction to 2D-Problems: U = U (x1 , x3 ) =⇒ Decoupling of the 3D-problem into a plane strain-state problem for (u 1 , u3 , ϕ) and anti-plane strain-state problem for u2 . Hookes law for the in-plane state (γ21 = γ22 = γ23 = 0, E2 = 0, U = (u1 , u3 , ϕ)> ): 1 0 σ11 c11 Bσ33 C Bc13 B C B B C B Bσ13 C = B 0 B C B @ D1 A @ 0 e31 D3 0 c13 c33 0 0 e33 0 0 c44 e15 0 0 0 −e15 ε11 0 10 −e31 ∂1 B −e33 C CB 0 CB 0 C B ∂3 CB 0 A@ 0 ε33 0 0 ∂3 ∂1 0 0 1 0 0 1 C 0 C u1 CB C 0 C @u3 A = ABU. C −∂1 A ϕ −∂3 Hooke’s law for the out-of-plane strain state (γ11 = γ33 = γ13 = 0, E1 = E3 = 0): σ23 σ21 ! = c44 0 0 c11 −c12 2 ! ∇u2 = A2 B2 u2 . 2D Field equations: −B > ABU = f, U = (u1 , u3 , ϕ), −B2T A2 B2 u2 = f2 . Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation 2D Total energy Page 7 Elasto-electrical energy (electric enthalpy): Ê = 1 2 R Ω ABU · BU dy − Exterior energy: F = Total energy: R Ω R f U dy + Ω R M BU · (−∇ϕ)dy + Ω 1 2 R Ω A2 B2 u2 · B2 u2 dy f2 u2 dy Π = Ê − F + D̂ Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation 2D Total energy Page 7 Elasto-electrical energy (electric enthalpy): Ê = 1 2 R Ω ABU · BU dy − Exterior energy: F = Total energy: R Ω R f U dy + Π = Ê − F + D̂ Ω R M BU · (−∇ϕ)dy + Ω 1 2 R Ω A2 B2 u2 · B2 u2 dy f2 u2 dy PSfrag replacements supp Θ y3 Straight crack propagation in y1 -direction, Ωδ = domain with crack of the length l + δ, Ω= domain with crack of the length l, Πδ =total energy in Ωδ . Γ+ Γ− δ Crack perpendicular to the polarisation in y3 direction Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation y1 Energy release rate Griffith criterion: Page 8 dΠδ |δ=0 = 0 dδ Assume D̂δ = 2δγ̂, γ̂ = γ̂(σc , Dc ), is known, then we have to calculate the Energy Release Rate ERR = d(Eδ −Fδ ) |δ=0 dδ = limδ→0 (Eδ −Fδ )−(E0 −F0 ) δ Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Energy release rate Griffith criterion: Page 8 dΠδ |δ=0 = 0 dδ Assume D̂δ = 2δγ̂, γ̂ = γ̂(σc , Dc ), is known, then we have to calculate the Energy Release Rate ERR = d(Eδ −Fδ ) |δ=0 dδ = limδ→0 (Eδ −Fδ )−(E0 −F0 ) δ Derivation of formulas for the ERR Assume: Ωδ (x-coordinates) and Ω (y-coordinates) are connected by a mapping: ! ! ! y1 x1 Θ(x) = −δ , 0 y2 x2 where Θ ∈ C0∞ (Ωδ ), suppΘ ⊂ a neighborhood of the crack tip, Θ ≡ 1 near the crack tip. Note, that these mappings are diffeomorphisms for 0 < δ < δ0 , since ∂(y1 ,y2 ) = 1 − δ∂1 Θ > 0. (∂x1 ,x2 ) Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation The Griffith formula Matrix-vector notation for the energy R 1 Ê = Ω 2 Cγ · γ − eγ · E − 12 εE · Edy, e= 0 e31 0 e33 Page 9 e15 0 ! , γ = Div > u = elastic e. + piezo e. - electric e. Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation The Griffith formula Matrix-vector notation for the energy R 1 Ê = Ω 2 Cγ · γ − eγ · E − 12 εE · Edy, e= 0 e31 0 e33 Page 9 e15 0 ! , γ = Div > u = elastic e. + piezo e. - electric e. Theorem (Griffith formula) ERR = R 0 ∂1 Θ 0 C 1 u + Cγ · γ∂1 θ) dy ∂ ∂ 3 ΘC 1 2 A B B 0 (−Cγ · Ω @ ∂3 Θ + R Ω (εE · ∇ΘE1 − 12 εE · E∂1 Θ) dy 0 − − R elastic part ∂1 Θ ∂1 Θ B + Ω eγE1 · ∇Θ + e B @ 0 ∂3 Θ R 1 0 R Ω A2 ∇u2 ∂1 u2 · ∇Θdy + Ω R electric part 1 C ∂ 3 ΘC A ∂1 u · E − eγ · E∂1 Θ dy ∂1 Θ coupled part U ∂1 (f Θ)dy exterior forces 1 Ω 2 A2 ∇u2 · ∇u2 ∂1 Θdy − Ω R u2 ∂1 (f2 Θ)dy antiplane part Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation The Griffith formula Proof: • • • Ideas from Khludnev/Sokolowski 99/00. R R Transformation of the energy integrals Ω · · · dx into Ω · · · dy. δ convergence: kUδ − U0 kH 1 (Ω) → 0, kfδ − f0 kL2 (Ω) → 0. Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Page 10 The Griffith formula Proof: • • • Ideas from Khludnev/Sokolowski 99/00. R R Transformation of the energy integrals Ω · · · dx into Ω · · · dy. δ convergence: kUδ − U0 kH 1 (Ω) → 0, kfδ − f0 kL2 (Ω) → 0. Remarks: Formula is independent of the choice of Θ. Integration on supp Θ only! Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Page 10 The J-integral Page 11 Theorem ( J-integral) R R R R ERR = Γ W n1 ds − Γ N σ · ∂1 uds + Γ DE1 · nds− Γ U · f n1 ds + R 1 A ∇u2 Γ 2 2 · ∇u2 n1 ds − R A ∇u2 ∂1 u2 · nds − Γ 2 provided f ≡ const near the crack tip. R Γ u2 f2 n1 ds, Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation The J-integral Page 11 Theorem ( J-integral) R R R R ERR = Γ W n1 ds − Γ N σ · ∂1 uds + Γ DE1 · nds− Γ U · f n1 ds + R 1 A ∇u2 Γ 2 2 · ∇u2 n1 ds − R A ∇u2 ∂1 u2 · nds − Γ 2 provided f ≡ const near the crack tip. σ = Cγ − e> E n1 0 0 n3 Γ u2 f2 n1 ds, Γ D = eγ + εE N= R n3 n1 ! PSfrag replacements Ω∗ W = 12 Cγ · γ − eγ · E − 12 εE · E Proof: Partial integration Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation The J-integral The Griffith criterion yields d(Ê − F + D̂)δ dΠδ |δ=0 = |δ=0 = 0 dδ dδ Assume, D̂δ = 2δγ̂. Therefore dD̂δ | dδ δ=0 = 2γ̂(σc , Dc ). The Griffith fracture criterion reads: Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Page 12 The J-integral The Griffith criterion yields d(Ê − F + D̂)δ dΠδ |δ=0 = |δ=0 = 0 dδ dδ Assume, D̂δ = 2δγ̂. Therefore dD̂δ | dδ δ=0 = 2γ̂(σc , Dc ). The Griffith fracture criterion reads: The crack propagates, if – ERR ≥ critical value = 2γ̂(σc , Dc ). Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Page 12 Stress intensity factors Page 13 From the general theory of elliptic boundary value problems follows: 0 1 0 1 0 1 u1 u1 0 Bu C B 0 C Bu C B 2C B C B 2C U =B C=B C+B C= @u 3 A @ u 3 A @ 0 A 0 ϕ ϕ 0 s11 (ω) 1 0 s21 (ω) 1 0 s41 (ω) 1 0 1 0 C B 0 C B 0 C B 0 C B 3 1 B 1 B 1 B 1 Bs2 (ω)C C C C = c1 r 2 B 1 C + Ureg , C + c2 r 2 B 2 C + c4 r 2 B 4 C + c3 r 2 B @ s3 (ω) A @ s3 (ω) A @ s3 (ω) A @ 0 A 0 ϕ1 (ω) ϕ2 (ω) ϕ4 (ω) 3 where Ureg = O(r 2 ). Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 13 From the general theory of elliptic boundary value problems follows: 0 1 0 1 0 1 u1 u1 0 Bu C B 0 C Bu C B 2C B C B 2C U =B C=B C+B C= @u 3 A @ u 3 A @ 0 A 0 ϕ ϕ 0 s11 (ω) 1 0 s21 (ω) 1 0 s41 (ω) 1 0 1 0 C B 0 C B 0 C B 0 C B 3 1 B 1 B 1 B 1 Bs2 (ω)C C C C = c1 r 2 B 1 C + Ureg , C + c2 r 2 B 2 C + c4 r 2 B 4 C + c3 r 2 B @ s3 (ω) A @ s3 (ω) A @ s3 (ω) A @ 0 A 0 ϕ1 (ω) ϕ2 (ω) ϕ4 (ω) 3 where Ureg = O(r 2 ). Inserting this decomposition of U into the J-integral we get: ERR = P 2 a c c + a c ij i j 3 3 i,j=1,2,4 Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 14 1 The coefficients aij , ci can be calculated, if the singular vectors r 2 S i (ω) 0 1 0 2 0 4 0 1 1 1 1 s1 (ω) s1 (ω) s1 (ω) 0 B 0 C B 0 C B 0 C B 3 C 1 B 1 B 1 B 1 Bs2 (ω)C C C C r2 B 1 C C, r2 B 2 C, r2 B 4 C, r2 B @ s3 (ω) A @ s3 (ω) A @ s3 (ω) A @ 0 A 0 ϕ1 (ω) ϕ2 (ω) ϕ4 (ω) 1 and the so called dual singular vectors r − 2 S −i (ω), i = 1, 2, 3, 4, 0 −1 0 −2 0 −4 1 1 1 s1 (ω) s1 (ω) s1 (ω) B 0 C B 0 C B 0 C 1 B 1 B B C C C −1 − − −1 r 2 B −1 C , r 2 B −2 C , r 2 B −4 C, r 2 @ s3 (ω) A @ s3 (ω) A @ s3 (ω) A ϕ− 1(ω) ϕ−2 (ω) ϕ−4 (ω) are known. 1 0 Bs−3 (ω)C C B 2 C B @ 0 A 0 0 Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 14 1 The coefficients aij , ci can be calculated, if the singular vectors r 2 S i (ω) 0 1 0 2 0 4 0 1 1 1 1 s1 (ω) s1 (ω) s1 (ω) 0 B 0 C B 0 C B 0 C B 3 C 1 B 1 B 1 B 1 Bs2 (ω)C C C C r2 B 1 C C, r2 B 2 C, r2 B 4 C, r2 B @ s3 (ω) A @ s3 (ω) A @ s3 (ω) A @ 0 A 0 ϕ1 (ω) ϕ2 (ω) ϕ4 (ω) 1 and the so called dual singular vectors r − 2 S −i (ω), i = 1, 2, 3, 4, 0 −1 0 −2 0 −4 1 1 1 s1 (ω) s1 (ω) s1 (ω) B 0 C B 0 C B 0 C 1 B 1 B B C C C −1 − − −1 r 2 B −1 C , r 2 B −2 C , r 2 B −4 C, r 2 @ s3 (ω) A @ s3 (ω) A @ s3 (ω) A ϕ− 1(ω) ϕ−2 (ω) ϕ−4 (ω) are known. 1 0 Bs−3 (ω)C C B 2 C B @ 0 A 0 0 Stroh’s formalism is used by Lothe/Barnett(76), Deeg(80) to calculate the singular terms. Explicit closed form ?? In preparation: Computation of the singular terms by numerical solution of a quadratic eigenvalue problem (W.Geis) Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 15 Calculation of the coefficients c1 , c2 , c3 , c4 by Maz’ya-Plamenevski coefficient formulas (76): ci = bi R f ·r Ω −1 2 S −i dy + R 1 1 > − 2 −i > − 2 −i N ABU · r S − U · N ABr S ds ∂Ω bi = scaling constants. Shortly R R ci = bi Ω f ·S−i dy+ ∂Ω g·S−i −U ·N > ABS−i ds. Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 15 Calculation of the coefficients c1 , c2 , c3 , c4 by Maz’ya-Plamenevski coefficient formulas (76): ci = bi R f ·r Ω −1 2 S −i dy + R 1 1 > − 2 −i > − 2 −i N ABU · r S − U · N ABr S ds ∂Ω bi = scaling constants. Shortly R R ci = bi Ω f ·S−i dy+ ∂Ω g·S−i −U ·N > ABS−i ds. We have assumed, that!the normal mechanical and electric stresses σ g = N > ABU = N > = 0. D Using FEM and BEM the coefficients c1 can be computed by postprocessing at least for linear elasticity. Maybe, it can be done for piezoelectric ceramics in a similar way. Note, the coefficients ci are fixed numbers, depending on the volume and surface loads. Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 16 We remind of the K-factors in linear ! isotropic elasticity (plane strain): ! ω ω √ √ 1 1 sin( 2 )(κ + 2 + cos ω) cos( 2 ) KI r KII r 1 2 2 2 √ √ r S = 2µ 2π (κ − cos ω) S = , r 2µ 2π sin( ω2 ) cos( ω2 )(κ − 2 + cos ω 0 1 1 σ11 B 1 C Bσ C @ 22 A 1 σ12 = KI cos( ω ) 2 √ 2πr 0 1 B B1 @ 1 3ω − sin( ω 2 ) sin( 2 )C 3ω C , + sin( ω 2 ) sin( 2 )A 3ω sin( ω 2 ) cos( 2 ) 0 1 2 σ11 B 2 C Bσ C @ 22 A 2 σ12 0 = 1 − sin( ω )(2 + cos( ω ) cos( 3ω 2 2 2 ))C KII B ω 3ω B C √ sin( ω A 2 ) cos( 2 ) cos( 2 ) 2πr @ ω ω 3ω cos( 2 )(1 − sin( 2 ) sin( 2 )) Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 16 We remind of the K-factors in linear ! isotropic elasticity (plane strain): ! ω ω √ √ 1 1 sin( 2 )(κ + 2 + cos ω) cos( 2 ) KI r KII r 1 2 2 2 √ √ r S = 2µ 2π (κ − cos ω) S = , r 2µ 2π sin( ω2 ) cos( ω2 )(κ − 2 + cos ω 0 1 1 σ11 B 1 C Bσ C @ 22 A 1 σ12 = KI cos( ω ) 2 √ 2πr 0 1 B B1 @ 1 3ω − sin( ω 2 ) sin( 2 )C 3ω C , + sin( ω 2 ) sin( 2 )A 3ω sin( ω 2 ) cos( 2 ) 0 1 2 σ11 B 2 C Bσ C @ 22 A 2 σ12 0 = √ √ 1 KI = limr→0 2πr σ22 (ω = 0) = limr→0 2πr σ22 (ω = 0) √ √ 2 KII = limr→0 2πr σ12 (ω = 0) = limr→0 2πr σ12 (ω = 0) Break down of this method in piezoelectricity ( Pak 92, Park/Sun 95) or anisotropic elastic case: √ √ lim lim 2πr σ.. (r, ω) 6= lim lim 2πr σ.. (r, ω) r→0 ω→0 1 − sin( ω )(2 + cos( ω ) cos( 3ω 2 2 2 ))C KII B ω 3ω B C √ sin( ω A 2 ) cos( 2 ) cos( 2 ) 2πr @ ω ω 3ω cos( 2 )(1 − sin( 2 ) sin( 2 )) ω→0 r→0 Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 17 These authors have investigated an infinite piezoelectric medium containing a center crack with far-field loading. They observed that for ω = 0 the stress and electrial fields are not coupled. Citation Park/Sun 95: This leads us to conclude that stress intensity factor is not suitable as fracture criterion for piecielectric materials. They used the mechanical part of the energy release rate (crack closure integral) instead. Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Stress intensity factors Page 17 These authors have investigated an infinite piezoelectric medium containing a center crack with far-field loading. They observed that for ω = 0 the stress and electrial fields are not coupled. Citation Park/Sun 95: This leads us to conclude that stress intensity factor is not suitable as fracture criterion for piecielectric materials. They used the mechanical part of the energy release rate (crack closure integral) instead. Mathematical point of view: To overcome these difficulties use the correct formulas for the computation of the stress intensity factors! Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation Conclusion Page 18 • Crack growth in piezoceramics can be enhanced or retarded by an electric field, depending on its magnitude and direction. In particular, if the crack is perpendicular to the poling direction, the resulting field equations for the mechanical and electric fields are strongly coupled. • The Griffith criterion, based on the total energy balance, is discussed. The energy release rate is given by a Griffith formula from which the J-integral follows. The influence of volume forces (e.g. temperature) is regarded. Surface forces (tractions, charges) can be considered too. • It is possible to express the total energy release rate by stress intensity factors in a correct way. • Since the computation of the stress intensity factors demands the knowledge of the dual singular terms, it seems to be more efficient to compute the J-integral. • Numerical experiments should be done in future. Universität Stuttgart, Institut für Angewandte Analysis und Numerische Simulation