Structural Dynamics 7/29/2005 Dynamic Analysis 1 Spring-Mass system subjected to a time dependent load. k F(t) m 7
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Structural Dynamics 7/29/2005
Dynamic Analysis
1
Spring-Mass system subjected to a time dependent load.
k F(t) m
7/29/2005
Dynamic Analysis
2
Free-body diagram of the mass.
T = kx
F(t) m
7/29/2005
= Dynamic Analysis
m
ma = m&x&
3
F(t ) − k x = m &x& m &x& + k x = F(t ) 7/29/2005
Dynamic Analysis
4
Solution of D.E. is sum of homogeneous and particular solutions:
Homogeneous :
F(t ) = 0 m &x& + k x = 0 7/29/2005
Dynamic Analysis
5
Let : k ω = m Then : 2
&x& + ω x = 0 2
ω2 is the natural circular frequency 7/29/2005
Dynamic Analysis
6
2π τ= ω τ is the period (measured in seconds) 7/29/2005
Dynamic Analysis
7
Displacement due to simple harmonic motion.
xm
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τ
Dynamic Analysis
8
One Dimensional Bar Element
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Dynamic Analysis
9
Step 1 - Select Element Type dˆ1x ˆf e (t ) 1x
1
2
dˆ 2 x
xˆ
ˆf e (t ) 2x
L E - modulus of elasticity A - cross-sectional area ρ - mass density 7/29/2005
Dynamic Analysis
10
Step 2 - Select a Displacement Function uˆ = a1 + a 2 xˆ uˆ = N 1dˆ1x + N 2dˆ 2 x xˆ N1 = 1 − L xˆ N2 = L 7/29/2005
Dynamic Analysis
11
Step 3 - Define Strain/Displacement and Stress/Strain Relationships
{}
ˆ ∂ u {ε x } = ˆ = [B ] dˆ ∂x 1 1 ⎡ ⎤ [B ] = ⎢ − ⎣ L L ⎥⎦ ˆ ⎫ ⎧ d dˆ = ⎨ 1x ⎬ ˆ d ⎩ 2x ⎭
{}
{σ} = [D ]{ε x } = [D ][B ]{dˆ} 7/29/2005
Dynamic Analysis
12
Step 4 - Derive Element Stiffness and Mass Matrices and Equations With time dependent loading
ˆf ≠ fˆ 1x 2x 7/29/2005
Dynamic Analysis
13
Newton’s Second Law
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Dynamic Analysis
14
NODAL EQUILIBRIUM EQUATIONS
ˆ d ∂ e 1x ˆf = fˆ + m 1x 1x 1 2 ∂t 2ˆ ∂ d e 2x ˆf = fˆ + m 2x 2x 2 2 ∂t 2
7/29/2005
Dynamic Analysis
15
m1 and m2 are obtained by lumping the total mass of the bar equally at the two nodes
ρAL m1 = 2 ρAL m2 = 2 7/29/2005
Dynamic Analysis
16
Lumped Mass Model dˆ1x fˆ1ex (t )
1
m1
2
m2
xˆ
dˆ 2 x fˆ2ex (t )
L
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Dynamic Analysis
17
Equilibrium in Matrix Form e ˆ ⎧⎪f1x ⎫⎪ ⎧⎪fˆ1x ⎫⎪ ⎡m 1 ⎨ˆ e ⎬ = ⎨ˆ ⎬ + ⎢ ⎪⎩f 2 x ⎪⎭ ⎪⎩f 2 x ⎪⎭ ⎣ 0
7/29/2005
Dynamic Analysis
⎧ ∂ dˆ1x ⎫ ⎪ ⎪ 2 0 ⎤⎪ ∂ t ⎪ ⎨ ˆ ⎬ ⎥ m 2 ⎦ ⎪ ∂ d 2x ⎪ 2 ⎪⎩ ∂ t ⎪⎭
18
Equilibrium in Matrix Form
& & ˆf (t ) = kˆ dˆ + [m ˆ ˆ] d e
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Dynamic Analysis
19
Defining Terms ⎡ 1 − 1⎤ AE [k ] = ⎢ ⎥ L ⎣− 1 1 ⎦ ρAL ⎡1 0 ⎤ [m ] = ⎥ ⎢ 2 ⎣0 1 ⎦ dˆ &ˆ& ∂ 2 dˆ d = ∂ t2
{}
{}
7/29/2005
{}
Element Stiffness Matrix Element Lumped Mass Matrix Nodal Displaceme nts Nodal Accelerati ons
Dynamic Analysis
20
Consistent Mass Matrix
{}
{ }
& & X = −ρ uˆ e
{f b } = ∫∫∫ [N ] {X} dV T
V
{f b } = − ∫∫∫ ρ[N ]
T
{}
&uˆ& dV
V
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Dynamic Analysis
21
Consistent Mass Matrix
ˆ {uˆ} = [N ] d &uˆ = [N ] dˆ& & & &uˆ& = [N ] dˆ 7/29/2005
Dynamic Analysis
22
Consistent Mass Matrix
{}
&ˆ& {f b } = − ∫∫∫ ρ[N ] [N ] d dV T
V
{}
&ˆ& {f b } = −[mˆ ] d
[mˆ ] = ∫∫∫ ρ[N ] [N ] dV T
V
7/29/2005
Dynamic Analysis
23
Consistent Mass Matrix Bar Element [mˆ ] = ∫∫∫ ρ[N ] [N ] dV T
V
⎧1 − xˆ ⎫ ⎪ L ⎪ ⎡ xˆ [mˆ ] = ∫∫∫ ρ⎨ xˆ ⎬ ⎢1 − V ⎪ ⎪⎣ L ⎩ L ⎭ xˆ ⎫ L ⎧1 − ⎪ L ⎪ ⎡ xˆ [mˆ ] = ρ A ∫ ⎨ xˆ ⎬ ⎢1 − 0 ⎪ ⎪⎣ L ⎩ L ⎭ 7/29/2005
Dynamic Analysis
xˆ ⎤ dV L ⎥⎦ xˆ ⎤ dxˆ L ⎥⎦ 24
Consistent Mass Matrix Bar Element ˆ ˆ ⎡ x x ⎛ ⎞ ⎛ ⎞ L ⎜1 − 1 − ⎜ ⎟ ⎢⎝ L ⎠⎝ L ⎟⎠ [mˆ ] = ρ A ∫ ⎢ ˆ ˆ x x ⎛ ⎞ ⎛ ⎞ 0 ⎢ ⎜1 − ⎟⎜ ⎟ ⎣ ⎝ L ⎠⎝ L ⎠ ρ A L ⎡2 [mˆ ] = ⎢ 6 ⎣1 7/29/2005
Dynamic Analysis
⎛⎜1 − xˆ ⎞⎟⎛⎜ xˆ ⎞⎟ ⎤ ⎝ L ⎠⎝ L ⎠ ⎥ dxˆ ⎥ ⎛⎜ xˆ ⎞⎟⎛⎜ xˆ ⎞⎟ ⎥ ⎝ L ⎠⎝ L ⎠ ⎦ 1⎤ ⎥ 2⎦ 25
STEP 5 - Assemble the Global Equations and Apply B.C.’s
& & {F(t )} = [K ]{d} + [M ]{d}
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Dynamic Analysis
26
& & {F(t )} = [K ]{d} + [M ]{d} Now must solve coupled set of ODE’s instead of set of linear algebraic equations!
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Dynamic Analysis
27
Consistent Mass Matrix
[m ] = ∫∫∫ ρ[N ] [N ] dV T
V
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Dynamic Analysis
28
Beam Element yˆ , vˆ ˆ1 φˆ 1 , m
1
xˆ
fˆ1y , dˆ 1y
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2 φˆ , m 2 ˆ 2 L
Dynamic Analysis
fˆ2y , dˆ 2y
29
Shape Functions
( 2x − 3x L + L ) L3 1 3 ( N2 = xˆ L − 2xˆ 2 L2 + xˆL3 ) 3 L 1 ( − 2xˆ 3 + 3xˆ 2 L ) N3 = 3 L 1 3 2 2 ˆ ˆ ( N4 = x L−x L ) 3 L N1 =
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1
3 ˆ
2 ˆ
Dynamic Analysis
3
30
Shape Functions 1.000
N1 0.500
N3
N2 L
0.000
N4
0 -0.500 7/29/2005
Dynamic Analysis
31
Consistent Mass Matrix
[m] = ∫∫∫ ρ[N] [N] dV T
V
22L ⎡ 156 ⎢ 22L 2 4 L m [m] = ⎢ 420 ⎢ 54 13L ⎢ 2 ⎣− 13L − 3L 7/29/2005
Dynamic Analysis
− 13L ⎤ 2 ⎥ − 3L ⎥ 156 − 22L ⎥ 2 ⎥ − 22L 4L ⎦ 54 13L
32
Lumped Mass Matrix ⎡1 ⎢ 0 ⎢ m [m] = ⎢0 2⎢ ⎢0 ⎢⎣ 7/29/2005
0 2 αL 210 0
1
0
0
Dynamic Analysis
0 0
0 ⎤ ⎥ 0 ⎥ ⎥ 0 ⎥ 2 αL ⎥ 210 ⎥⎦ 33
Lumped Mass Matrix 2nd and 4th terms account for rotary inertia. α = 0 if this is ignored. α = 17.5 if mass moment of inertia of bar spinning about one end is selected
⎛ m ⎞⎛ L ⎞ ⎜ ⎟⎜ ⎟ 2 ⎠⎝ 2 ⎠ ⎝ I= 3 7/29/2005
Dynamic Analysis
2
34
Consistent Mass Matrix - CST ⎡Q 0 ⎤ [m] = ⎢ ⎥ 0 Q ⎣ ⎦ ⎡ 2 1 1⎤ u1 m⎢ ⎥ [Q] = ⎢1 2 1⎥ u 2 12 ⎢⎣1 1 2⎥⎦ u 3
For each degree of freedom
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Dynamic Analysis
35
Consistent Mass Matrix - CST ⎡2 ⎢0 ⎢ ρAt ⎢1 [m] = ⎢ 12 ⎢ 0 ⎢1 ⎢ ⎢⎣ 0 7/29/2005
0 1 0 1 0⎤ ⎥ 2 0 1 0 1⎥ 0 2 0 1 0⎥ ⎥ 1 0 2 0 1⎥ 0 1 0 2 0⎥ ⎥ 1 0 1 0 2⎥⎦ Dynamic Analysis
36
Lumped Mass Matrix - CST ⎡Q 0 ⎤ [m] = ⎢ ⎥ 0 Q ⎣ ⎦ ⎡1 0 0⎤ u 1 m⎢ ⎥ [Q] = ⎢0 0 1⎥ u 2 3 ⎢⎣0 0 1⎥⎦ u 3
7/29/2005
Dynamic Analysis
37
Lumped Mass Matrix - CST ⎡1 ⎢0 ⎢ ρAt ⎢0 [m] = ⎢ 3 ⎢0 ⎢0 ⎢ ⎢⎣0 7/29/2005
0 0 0 0 0⎤ ⎥ 1 0 0 0 0⎥ 0 1 0 0 0⎥ ⎥ 0 0 1 0 0⎥ 0 0 0 1 0⎥ ⎥ 0 0 0 0 1⎥⎦
Dynamic Analysis
38
Consistent Mass Matrix - Quad ⎡Q 0 ⎤ [m] = ⎢ 0 Q ⎥ ⎢⎣ ⎥⎦ ⎡4 2 ⎢2 4 [Q] = m ⎢ 36 ⎢1 2 ⎢ ⎣2 1 m = ρAt
7/29/2005
Dynamic Analysis
1 2⎤ ⎥ 2 1⎥ 4 2⎥ ⎥ 2 4⎦
39
Consistent Mass Matrix - Quad ⎡4 ⎢0 ⎢ ⎢2 ⎢ m ⎢0 [m] = ⎢ 36 1 ⎢ ⎢0 ⎢2 ⎢ ⎢⎣0 7/29/2005
0 2 0 1 0 2 0⎤ ⎥ 4 0 2 0 1 0 2⎥ 0 4 0 2 0 1 0⎥ ⎥ 2 0 4 0 2 0 1⎥ 0 2 0 4 0 2 0⎥ ⎥ 1 0 2 0 4 0 2⎥ 0 1 0 2 0 4 0⎥ ⎥ 2 0 1 0 2 0 4⎥⎦ Dynamic Analysis
40
Hybrid Methods Attempts have been made to combine consistent and lumped mass approaches to achieve some of the benefits of each!
7/29/2005
Dynamic Analysis
41
HRZ Lumping 1. Hinton, Rock, and Zienkiewicz 2. Compute the diagonal terms of consistent
mass matrix. 3. Compute total mass of element, m 4. Compute s by adding diagonal coefficients associated with translational D-O-F that are in same direction. 5. Scale all diagonal coefficients by multiplying by m/s 7/29/2005
Dynamic Analysis
42
HRZ - Bar Element ρ A L ⎡2 1⎤ [mˆ ] = ⎢ ⎥ 6 ⎣1 2⎦ m = ρAL ρAL s = 4× 6 m 3 = s 2 ρ A L ⎡3 0⎤ [mˆ ] = ⎢ ⎥ 6 ⎣ 0 3⎦ 7/29/2005
Dynamic Analysis
43
HRZ - Beam Element 22L 54 − 13L ⎤ ⎡ 156 ⎢ 22L 2 2 ⎥ 4 13 3 − L L L m ⎥ [m] = ⎢ 420 ⎢ 54 13L 156 − 22L ⎥ ⎢ 2 2 ⎥ ⎣− 13L − 3L − 22L 4L ⎦ m = ρAL ρAL s = 312 × 420 m = 420 s 312 7/29/2005
Dynamic Analysis
44
HRZ - Beam Element ⎡ 420 ⎢ 312 × 156 ⎢ ⎢ 0 m ⎢ [mˆ ] = 420 ⎢ 0 ⎢ ⎢ ⎢ 0 ⎢⎣
7/29/2005
0
0
420 × 4 L2 312
0
0
420 × 156 312
0
0
Dynamic Analysis
⎤ 0 ⎥ ⎢ 39 ⎥ ⎥ ⎢ ⎥ 2 ⎥ 0 L ⎢ ⎥ m ⎥= ⎢ ⎥ ⎥ 78 ⎢ 39 ⎥ 0 ⎥ ⎢ ⎥ ⎥ 2 ⎢ L 420 ⎣ ⎥⎦ 2 ⎥ × 4L ⎥⎦ 312
45
HRZ – Quadratic Serendipity 1 36
3 76
8 36
16 76 3x3 Gauss Rule
7/29/2005
2x2 Gauss Rule
Dynamic Analysis
46
HRZ – Quadratic Lagrangian 1 36
1 36 4 36
16 36
16 36
3x3 Gauss Rule
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4 36 2x2 Gauss Rule
Dynamic Analysis
47
% error in natural frequencies of a thick simply-supported plate. Half of the plate modeled with 8-noded 24 d-o-f elements Mode m n 1 1 2 1 2 2 3 1 3 2 3 3 4 2
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Type of Mass Matrix Consistent (%) HRz Lumping (%) Ad Hoc Lumping (%) 0.11 0.32 0.32 0.4 0.45 0.45 0.35 2.75 4.12 5.18 0.05 5.75 4.68 2.96 10.15 13.78 5.18 19.42 16.88 1.53 31.7
Dynamic Analysis
48
Optimal Lumping Only translational d-o-f Based on consistent mass matrix Use appropriate quadrature rule Chose integration points to coincide with nodal locations [m] will be diagonal
7/29/2005
Dynamic Analysis
49
Let p be the highest order complete
polynomial in shape function N let m be the highest order derivative in strain energy (m = 1 elasticity, m = 2 bending) Chose quadrature rule with degree of precision 2(p-m)
7/29/2005
Dynamic Analysis
50
Three noded bar element p=2 m=1 2(p-m) = 2 Three point quadrature rule. Newton -Cotes has points at the nodes. (Simpson’ Rule) b
⎡1 ⎤ 4 ⎛b+a⎞ 1 ∫a f (x)dx = (b − a )⎢⎣ 6 f (a ) + 6 f ⎜⎝ 2 ⎟⎠ + 6 f (b )⎥⎦ 7/29/2005
Dynamic Analysis
51
1
m ij = ρA ∫ N i N jdx = ∫ N i N j J dξ −1
L J= 2 L 4 1 ⎡1 ⎤ m ij = ρA (1 − (− 1))⎢ N i (− 1)N j (− 1) + N i (0)N j (0 ) + N i (1)N j (1)⎥ 2 6 6 ⎣6 ⎦ i ≠ j m ij = 0
⎡1 0 0⎤ ρAL ⎢ ⎥ [m] = 0 1 0⎥ ⎢ 6 ⎢⎣0 0 4⎥⎦ 7/29/2005
1
Dynamic Analysis
3
2
52
Serendipity 1 − 12 1 3
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Dynamic Analysis
53
Lagrangian 1 36
4 9
7/29/2005
Dynamic Analysis
1 9
54
Mass Matrices Product [m]{a} must yield the correct total force on an element (F = ma) when {a} represents a rigidbody translational acceleration. Consistent mass matrices, [m] and [M] are positive definite. Lumped mass matrix is positive semi-definite when zero terms appear on main diagonal. Lumped mass matrix is indefinite when negative terms appear on main diagonal.
7/29/2005
Dynamic Analysis
55
Mass Matrices Special treatment may be needed to handle the last two cases.
7/29/2005
Dynamic Analysis
56
Best Type ? 1. Consistent matrices usually
more accurate for flexural problems. 2. Consistent matrices give upper bounds on natural frequencies.
7/29/2005
Dynamic Analysis
57
Best Type ? 1. Lumped matrices usually give natural 2. 3. 4. 5.
frequencies less than exact values. Simpler to form. Occupy less storage. Require less computational effort. Usually more important in time-history than in vibration problems.
7/29/2005
Dynamic Analysis
58
Damping 1. Structural damping is not viscous. 2. Due to mechanisms such as hysteresis and 3. 4. 5. 6.
slip in connections. Mechanisms not well understood. Awkward to incorporate into structural dynamic equations. Makes equations computationally difficult. Effects usually approximated by viscous damping.
7/29/2005
Dynamic Analysis
59
Types of Damping Models Phenomenological Damping Methods
(models actual dissipative mechanisms) Ø Ø Ø
Elastic-Plastic Hysteresis Loss Structural Joint Friction Material Micro-cracking
Spectral Damping Methods Ø Ø
7/29/2005
Introduce Viscous Damping Relies on Fraction of Critical Damping Dynamic Analysis
60
Critical Damping ξ
Fraction of Critical Damping ξ=1
Critical Damping
Critical Damping marks the transition between oscillatory and non- oscillatory response of a structure
7/29/2005
Dynamic Analysis
61
Critical Damping Ratio 0 .5 % ≤ ξ ≤ 5 % 2% ≤ ξ ≤ 15% 2% ≤ ξ ≤ 15%
Steel Piping Bolted or riveted steel structures Reinforced or Prestresses Concrete
Actual value may depend on stress level. 7/29/2005
Dynamic Analysis
62
Rayleigh or Proportional Damping Damping matrix is a linear combination of stiffness and mass matrices:
[C] = α [K ] + β [M ] 7/29/2005
Dynamic Analysis
63
Rayleigh or Proportional Damping [C] is orthogonal damping matrix. Modes may be uncoupled by eigenvectors associated with undamped problem.
1⎛ β⎞ ξ = ⎜αω− ⎟ 2⎝ ω⎠ 7/29/2005
Dynamic Analysis
64
If critical damping ratio is known at two frequencies then: β⎞ 1⎛ ξ = ⎜αω− ⎟ 2⎝ ω⎠ (ξ 2 ω 2 − ξ 1 ω1 ) α=2 2 2 ω 2 − ω1
(
β = 2 ω1 ω 2 7/29/2005
)
(ξ 1 ω 2 − ξ 2 ω1 )
(ω
2 2
Dynamic Analysis
−ω
2 1
)
65
Natural Frequencies and Mode Shapes Undamped, Unforced Response
{D} = {D }sin ωt
{D& } = ω{D }cos ωt {D&& } = − ω {D }sin ωt 2
{D }
amplitudes of nodal d - o - f
ω circular frequency ω f = 2π 7/29/2005
( Hz ) Dynamic Analysis
66
Results in generalized eigenproblem
([K ] − λ [M ]){D } = {0} λ=ω
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2
Dynamic Analysis
67
Trivial Solution:
[K ] − λ [M ]
≠0
{D } = 0
7/29/2005
Dynamic Analysis
68
Nontrivial Solution:
[K ] − λ[M ]
{D} ≠ 0
7/29/2005
Dynamic Analysis
=0
69
λi
{D }
i
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≡ Roots of Characteristic Polynomial (eigenvalues) ≡ Associated
Dynamic Analysis
Eigenvectors
70
ω i Natural Frequencies
{D }
i
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Normal Modes
Dynamic Analysis
71
Natural Frequencies [K] and [M] n x n then there are n eigenvalues and n eigenvectors [K] and [M] positive definite then eigenvalues are
all positive Mii = 0 infinite eigenvalue Mii < 0 negative eigenvalue - imaginary frequency Use condensation to remove ith equation if Mii = 0
7/29/2005
Dynamic Analysis
72
Rayleigh Quotient
{ D} [K ]{D} λ= {D} [M ]{D} T
T
{D}
[K ] symmetric [M ] positive definite th
approximat ion to i eigenvector
λ approximat ion to i eigenvalue th
7/29/2005
Dynamic Analysis
73
Rayleigh Quotient
λ min
{ v } [K ]{v } ≤ ≤ λ max T {v } [M ]{v }
λ min
smallest eigenvalue
λ max
l arg est eigenvalue
T
7/29/2005
Dynamic Analysis
74
Modal Methods When [K], [C], [M] are known and time independent the problem is linear.
{
ext & & & [M ]{D }+ [C ]{D }+ [K ]{D} = R
{D& (0 )}, {D (0 )} 7/29/2005
}
given as initial conditions Dynamic Analysis
75
Modal Methods Assume orthogonal damping, such as Rayleigh Damping. Modes can be uncoupled:
{D } [M ]{D } = 0 {D } [K ]{D } = 0 {D } [C ]{D } = 0 T i
j
T i
j
T i
j
i≠j 7/29/2005
Dynamic Analysis
76
{D } [M ]{D } = 1 {D } [K ]{D } = ω {D } [C ]{D } = 2 ξ ω T i
i
T i
T i
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2 i
i
i
Dynamic Analysis
i
i
77
Eigenvectors are linearly independent
[φ] = matrix of {Z} 7/29/2005
eigenvectors (mode shapes) {D} = [φ]{Z} modal amplitudes Dynamic Analysis
78
Substitute into:
{
ext & & & [M ]{D }+ [C ]{D }+ [K ]{D} = R {D& (0 )}, {D (0 )} given
7/29/2005
Dynamic Analysis
}
79
{
ext & & & [M ][φ ]{Z }+ [C ][φ ]{Z }+ [K ][φ ]{Z } = R [φ ]{Z& ( 0 ) } = {D& (0 )}
[φ ]{Z ( 0 ) } = {D (0 )}
7/29/2005
Dynamic Analysis
given
80
}
Mode Displacement Method
[ ]
2 & & & [I ]{Z }+ [ξ ]{Z }+ ω {Z } = {p}
7/29/2005
Dynamic Analysis
81
Mode Displacement Method Pre-multiply by [φ]T T & & [M ][φ ]{Z }+ [φ ] [C ][φ ]{Z& }
[φ ] T T ext + [φ ] [K ][φ ]{Z } = [φ ] {R } [φ ]{Z& ( 0 ) } = {D& (0 )} [φ ]{Z ( 0 ) } = {D (0 )} given T
7/29/2005
Dynamic Analysis
82
Mode Displacement Method
[φ ] [M ][φ ] = [I ] T [φ ] [C ][φ ] = [ξ ] T 2 [φ ] [K ][φ ] = [ω ] T
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Dynamic Analysis
83
Mode Displacement Method
[ ]
2 & & & [I ]{Z }+ [ξ ]{Z }+ ω {Z } = {p}
7/29/2005
Dynamic Analysis
84
Modes Uncouple:
[ ]
2 & & & [I ]{Z }+ [ξ ]{Z }+ ω {Z } = {Z } &Z& + 2 ξ ω Z & + ω 2 Z = p i = 1, n i
7/29/2005
i
i
i
i
Dynamic Analysis
i
85
[φ ]{Z& ( 0 ) } = {D& (0 )} [φ ]{Z ( 0 ) } = {D (0 )} T T & [φ ] [M ][φ ]{Z ( 0 ) } = [φ ] [M ]{D& (0 )} T & [I ] {Z ( 0 ) } = [φ ] [M ]{D& (0 )} T & {Z ( 0 ) } = [φ ] [M ]{D& (0 )} T {Z ( 0 ) } = [φ ] [M ]{D (0 )} 7/29/2005
Dynamic Analysis
86
Reduce size of problem:
m