Lateral Buckling in Steel-concrete Composite Beams
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7/25/2019 Lateral Buckling in Steel-concrete Composite Beams
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Lateral buckling in steel-concrete composite beams
Renato José Vacas Guedes
Abstract
This dissertation presents results that concerns to a study about composite steel-concrete
beams, where the steel area is a metallic I section, however the stability problems of themetallic section are the main subject of this work, since this is one of the major problem when
concerning to metallic sections.
The Lateral Buckling problem is quite complex phenomena which evolutes in the hogging
moment area of the continue composite beams, to do an exact analysis of this problem would
be too hard and would be such a complex process, so to setting the value of Critical Moment
of the section it was used the formula present in the EN 1994-1-1, which is less complex
than the exact solution, and a posteriori used the Critical Moment to set the value of the
Lateral Buckling Moment . It will be developed a toolkit which enables us to set the value
of the Lateral Buckling Moment in a prompt way following the methodology used in the
EN 1994-1-1.
Keywords
Steel-concrete composite beams; Lateral torsional buckling; Critical moment; Uniform Lateral
Slenderness; continue composite beams; lateral buckling moment
1- Introduction
A composite structure is the one where two or more materials work together. The goal of this
connection is to get the best of the materials and make the new material better than the ones
that had originated it. The composite steel-concrete beam has been used with more regularity
lately in construction because they provide a fast, economic and structural solution.
In sagging moments the concrete slab is working on compression and the steel beam is working
on traction, when that happens the composite beam fulfills is potential because both materials
are tensioned in a way that their performance is better. On the other hand, if the beam is in a
hogging moment zone and the concrete are on traction, which isn’t good because the concrete
has a very low resistance to traction and will crack. The steel will be compressed and instability
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problems will developed in the beam. The instability problems develop on steel sections
because they are really slender. The concrete slab will increase the steel section resistance to
that phenomenon, because the concrete doesn’t enable the upper flange deformation and
consequently the web deformation is restrained to.
It will be developed an excel toolkit with the purpose of calculate de Lateral Buckling ResistantMoment (Mb,Rd) in a prompt way, following the methodology of EN 1994-1-1.
There are some authors that had developed this matter in the last years. Bradford (1981)
developed a method to calculate the critical moment (Mcr ). Dekker, Kemp and Trinchero (1995)
proposed a method to predict the buckling strength of the composite plain webbed beams.
Bradford (1998) analyzed the distortional buckling in I beams and developed a method
considering that the upper flange have the translation totally restrained and the lower is partially
restrained. Bradford and Kemp (2000) defined the buckling phenomenon of composite beams
as exclusive of the negative moments. Hanswille (2000) developed a method to calculate the
critical moment; this methodology is based on the U-frame inverted model where the steel beam
is laterally and elastically restrained by the concrete slab. Vrcelj and Bradford (2007) studied a
mode of restrained distorcional buckling (RDB) of composite beams, which involve a distortional
deformation of the web, the authors developed a finite element model to study the problem
(bubble augmented spline finite strip). Vrcelj and Bradford (2009) developed a method to
determinate the elastoplastic bifurcation load of composite beams based on the bubble
augmented spline finite strip, developed by the authors. Salah and Gizewjowski (2008)
developed a finite element model with the purpose of analyze the instability in the hogging
moment zone, they concluded that when the beam becomes longer the collapsing mode tend to
have lateral buckling collapse and not plastic.
2- Critical Moment evaluation methods
2.1- Hanswille method
The Hanswille method (2000) is based on the invert U-frame model (fig. 1), in which the steel
section has is rotation and translational movements restrained because the presence of the
concrete slab. The restrain of the slab is simulated by an analogy with the buckling of a
compression member on elastic foundation.
The method developed by Hanswille is based in the theory of Vlasov, where the warping
restrictions are included, plus the rotation restriction conferred by the concrete slab, and the
following differential equation represents the solution for the problem presented to Hanswille.
(1)
The previous expression origins the critical moment equations that Hanswille developed, where
equation (2) is for uniform moment and equation (3) is for non-uniform moment.
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(2)
(3)
Fig.2: U-frame inverted model[2]
2.2- Dekker et al method
The restrain that the web provides to the compression flange will influence the type of
deformation of the steel beam, introducing a distortional component when the beam deforms,
which doesn’t existed when the steel beam acted alone.
To simulate the restrain imposed by the web to the lower flange, Dekker developed an
approximated method based on the rigid web theory, with some differences to make possible
restrain the deformation of the upper flange and simulate the web flexion stiffness. The author
developed a method based on the critical moment of isolated I beams, using coefficients to
simulated the presence of the concrete slab.
(4)
The previous formula is the definition of the critical moment of an isolated steel beam, and with
the Dekker’s approximation some of the parameters are multiplied by coefficients (C1; C2; C3)
which simulate the presence of the slab.
(5)
2.3- Eurocode 4 method
In order to elaborate this study of the behavior of composite steel-concrete beams was
developed an Excel toolkit, based in the Eurocode 4 methodology.
The Eurocode 4 deals with the lateral buckling of continuous composite beams by reducing the
section moment resistance at the internal support to a lower value referred to the beam buckling
strength. Because the composite beam is one of several parallel members attached to the same
concrete slab, design is based on the inverted U-frame model. When the slab deforms under
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applied load, there is a tendency for the steel beams to rotate as a result of slab deformations
and additionally distort laterally. The slab may always be regarded as providing the full lateral
restraint to the upper flange of steel I-section.
Acording to the Anex B of ENV 1994-1-1 (CEN, 2000), the critical o moment is calculated based
on the inverted U-frame model, resulting in the following expression.
(6)
(7)
The Dekker’s formula is the most conservative method because of his assumption of the rigid
steel section, when he tries to simulate the beam behavior. So the rigidity of the section will
diminish the value of the critical moment. Hanswille considers constant the flexional transverse
stiffness and the torsional St. Venant constant, unlike Dekker. In the EC4 the approach is less
complex than the one developed by Hanswille, so it’s normal if the EC4 method is more
conservative.
3- Presentation of the model
3.1- Eurocode 4 model
The study object of this work is the composite steel-concrete beams and their tendency to have
lateral instability problems. With that in mind it was elaborated an Excel toolkit based on the
norm EN 1994-1-1 to imitate behavior of 2 and 3 span beams.
There are several parameters that control the lateral buckling in this study, see fig (2). The
parameters are provided to the toolkit and it turn back the value of critical moment (Mcr ),
normalized slenderness ( ), the reduction coefficient and the reduced resistant moment
(Mb,Rd). The program receives the data of the parameters defined above and generates de
areas, moments of inertia and flexure modules of the concrete, steel and composite sections.
After the program generates all this information, it’s operated a macro which will provide the
shear and resistant moment’s diagrams. Those diagrams will allow an analysis of the cracking
of the concrete slab and permit the decision of making a cracked or un-cracked analysis.
Those diagrams will allow an analysis of the cracking of the concrete slab and permit the
decision of making a cracked or un-cracked analysis.
A macro is created to develop a program of finite elements with the SAP2000. The concrete
slab effective width doesn’t remains constant along the span of the beam, so to mimic this
behavior the program generated two different width, one in the hogging zone and one other at
the sagging zone (fig. 3). The program uses a frame element to represent the beam, the frame
element is represented by a generic I section and 15 finite elements are use to simulate the
sagging zone at the outer span and 20 to simulate the other zones (fig. 4), to differentiate
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between the different beam width the program changes the moment of inertia of the section
generated. In fig. 5 it can be seen the out-put of the program.
Fig. 2: Composite steel-concrete beam transversal section.
Fig. 3: Determination of the effective width.
Fig. 5: Finite element model, frames.
Fig. 5: Sap2000 out-put.
Bc,eff
Bc
h c
bf
tw h
w
t f
h s , t
h s , l
As,l As,t
e
L AB LBC LCD
A B C D
0,75 L AB 0,25 L AB 0,25 LBC 0,50 LBC 0,25 LBC 0,25 LCD 0,75 LCD
e f f
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3.2- Models Comparison
3.2.1- 2-span beam
The three models used to calculate the critical moment will be compared in this chapter as can
be seen in fig. 6. The Hanswille method, excluding the fig. 6 (a), is the less conservative
method and with the increase of the web height is value is more far away then the other
methods. The Dekker method is more the conservative and the EC4 is in the middle. Even with
different values de graphics develop in the same way. So in a 2-span beam the method in study
is between the other to methods and presents similar results to the more conservative method,
therefore is concluded that the this method is good to predict the critical moment of a composite
2-span beam.
(a) (b)
(c) (d)Fig.6: Influence of thickness of the web in the value of the critical moment in a 2-span beams
for : (a) ; (b) ; (c) ; (d) .
4.2.2- 3-span beam
In fig. 7 the method of Eurocode 4 is compared to the Hanswille and the critical moments of
both methods are smaller when compared to the 2-span beam. Hanswille still are less
conservative then the Eurocode 4 approach and when the web height increases the critical
3500
4500
5500
6500
7500
8500
10 11 12 13 14
M o m e n t o C r í t i c o ,
M c r ( K N . m
)
Espessura da alma, tw (mm)
EC4 hw=420
Hanswille hw=420
Dekker hw=420
3500
5500
7500
9500
11500
13500
10 11 12 13 14 M o m e n t o C r í t i c o ,
M c r ( K N . m
)
Espessura da alma, tw (mm)
EC4 hw=515
Hanswille hw=515
Dekker hw=515
3500
4500
5500
6500
7500
8500
9500
10500
10 11 12 13 14
M o m e n t o C r í t i c o ,
M c r ( K N . M
)
Espessura da alma, tw (mm)
EC4 hw=470
Hanswille hw=470
Dekker hw=470
3500
5500
7500
9500
11500
13500
15500
17500
10 11 12 13 14
M o m e n t o C r í t i c o ,
M c r ( K N . m
)
Espessura da alma, tw (mm)
EC4 hw=560Hanswille hw=560Dekker hw=560
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moment values diverge on both methods, because in the Hanswille method critical moment had
a higher increase.
In all of the graphics critical value adopt the same development, increasing with the increase of
the web thickness. So in a 3-span beam the method in study as the same behavior than in the
2-span beam therefore is concluded that this method is good to predict the critical moment of acomposite 3-span beam.
(a) (b)
(c) (d)Fig. 7: Influence of web height in the value of critical moment of a 3-span composite beam, for:
(a) ; (b) ; (c) ; (d)
4- Parametrical Study
4.1- Influence of the parameters in normalized slenderness
In this chapter several parameters are analyzed and their influence in the process of lateral
buckling. And the analyzed parameters are web height and thickness, the flange width and
thickness, the concrete slab width, the span length, the overload, the concrete rupture strength
and the steel yield strength.
2000
2500
3000
3500
4000
4500
5000
10 11 12 13 14
M o m e n t o C r í t i c o ,
M c r ( K N . m
)
Espessura da alma, tw (mm)
EC4 hw=420
Hanswille hw=420
2500
3500
4500
5500
6500
7500
8500
10 11 12 13 14
M o m e n t o C
r í t i c o ,
M c r ( K N . m
)
Espessura da alma, tw (mm)
EC4 hw=515
Hanswille hw=515
25003000
3500
4000
4500
5000
5500
6000
6500
10 11 12 13 14
M o m e n t o C r í t i c o ,
M c r ( K N . m
)
Espessura da alma, tw (mm)
EC4 hw=470
Hanswille hw=470
2000
3500
5000
6500
8000
9500
11000
10 11 12 13 14
M o m e n t o C
r í t i c o ,
M c r ( K N . m
)
Espessura da alma, tw (mm)
EC4 hw=560
Hanswille hw=560
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Fig. 8: Web thickness influence in normalized slenderness Fig. 9: Overload influence in normalized slenderness
Fig. 10: Span length width influence in normalized Fig. 11: Steel yield strength influence in normalized
4.2- Proposed formulas to the normalized slenderness
4.2.1- 2-span beam
Fig. 12: hw/tw influence in normalized slenderness Fig. 13: tf /bf influence in normalized slenderness
0,20
0,30
0,40
0,50
0,60
0,70
0,80
10 11 12 13 14
N o r m a l i z
e d S l e n d e r n e s s ,
λ L T
Web thickness, tw (mm)
hw=420-2span hw=470-2spanhw=515-2span hw=560-2spanhw=420-3span hw=470-3spanhw=515-3span hw=560-3span
0,20
0,30
0,40
0,50
0,60
0,70
5 10 15 20 25 30 35 40 N o r m a l i z e d
S l e n d e r n e s s ,
λ L T
Overload, sc (KN/m2)
hw=420hw=470hw=515hw=560
0,20
0,30
0,40
0,50
0,60
3 4 5 6 N o r m a l i z e d S l e n d e r n e s s ,
λ L T
Span length , L (m)
hw=420-2spanhw=470-2spanhw=515-2spanhw=560-2span
0,20
0,30
0,40
0,50
0,60
0,70
0,80
235 275 315 355 N o r m a l i z e d S l e n d e r n
e s s ,
λ L T
Steel yield strength, f yd (MPa)
hw=420hw=470hw=515hw=560
0,30
0,35
0,40
0,45
0,50
30,0 35,0 40,0 45,0 50,0 55,0
N o r m a l i z e d S l e n d e r n e s s ,
λ L T
hw/tw
hw=420
hw=470
hw=515
hw=560Proposta
0,30
0,35
0,40
0,45
0,50
0,055 0,06 0,065 0,07 0,075 0,08 0,085 0,09 N o r m a l i z e
d S l e n d e r n e s s ,
λ L T
tf /bf
hw=420hw=470hw=515Proposta
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Fig. 14: 1/C4 influence in normalized slenderness Fig. 15: L influence in normalized slenderness
(13)
4.2.2- 3-span beam
Fig. 16: hw/tw influence in normalized slenderness Fig. 17: tf /bf influence in normalized slenderness
Fig. 18: f yd influence in normalized slenderness Fig. 19: L influence in normalized slenderness
(5.14)
0,30
0,35
0,40
0,45
0,50
3 4 5 6 N o r m a l i z e d
S l e n d e r n e s s ,
λ L T
L
hw=420
hw=470
hw=515
Proposta
0,40
0,50
0,60
0,70
30,0 35,0 40,0 45,0 50,0 55,0
E s b e l t e z a n o r m a l i z a d a ,
λ L T
hw/tw
hw=420
hw=470
hw=515
hw=560
0,30
0,40
0,50
0,60
0,70
0,055 0,06 0,065 0,07 0,075 0,08 0,085
E s b e l t e z a n o r m a l i z a d a ,
λ L T
tf/bf
hw=420
hw=470
hw=515
Proposta
0,30
0,40
0,50
0,60
0,70
3 4 5 6
E s b e l t e z a n o r m
a l i z a d a ,
λ L T
L
hw=420
hw=470
hw=515
Proposta0,40
0,50
0,60
0,70
235 275 315 355
E s b e l t e z a n o r m a l i z a d a ,
λ L T
f yd
hw=420
hw=470
hw=515
Proposta
0,30
0,40
0,50
0,60
0,70
0,04 0,045 0,05 0,055 0,06 0,065 0,07
N o r m a l i z e d S l e n d e r n e s s ,
λ L T
1/C4
hw=420
hw=470
hw=515
Proposta
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5- Conclusion future developments
The parameters with more influence in the process of lateral buckling are steel yield strength,
the web thickness and height and the length of the span. When the value of those parameters
increases they make a large variation in the value of the normalized slenderness. On the other
hand the flange doesn’t have much influence on the problem, although the width is more
important than the thickness of the flange. The slab is important to restrain the upper flange and
the web, a variation on the rupture strength of the concrete slab only make the slenderness
change when an elastic analysis is made. The overload it’s only important if it is applied in a
non-symmetrical way, which will change the moment diagram and change the C4 parameter.
In future developments should be developed a method to define the value of the normalized
slenderness of class 3 and 4 sections and of beams with 4 or more spans.
6- Bibliography
[1] EN 1993-1-1, Eurocode 3 Part 1-1: Design of steel structures – Part 1-1: General rules and
rules for buildings, CEN, Brussels 2005
[2] EN 1994-1-1, Eurocode 4: Design of composite steel and concrete structures, Part 1-1:
General rules for buildings, CEN, Brussels 2005
[3] Salah, W; Gizewjowski, M; M. A. 2008. Restrained distortional buckling of composite beams-
FE modeling of the behavior of steel-concrete beams in the hogging moment region, in Proc.
Eurosteel Conference, 2008, Graz, Austria, 1629-1634.
[4] Hanswille, G. 2000. Torsional buckling of composite beams, comparison of more accurate
methods with Eurocode 4, in Proc. Composite Construction in Steel and Concrete IV, 2000,
Banff, Alberta, Canada, 105-116. doi:10,1061/40616(281)10
[5] Dekker, N.; Kemp, A. R.; Trinchero P. 1995. Factors influencing the strength of continuous
composite beams in negative bending, Journal of Constructional Steel Research 34:262-185
[6] Gizewjowski, M.; Salah, W. 2010. Restrained distortional buckling strength of steel-concrete
composite beams – a review of current practice and new developments, in Proc, International
Conference, 2010, Vilnius, Lithuania, 604-612.
[7] Vrcelj, Z. e Bradford, M. A., 2006. Elastic Distortional Buckling of Continuous Restrained I-
section Beam-columns. Journal of Constructional Steel Research. 62:223-230.
[8] Vrcelj, Z. e Bradford, M. A., 2007. Elastic Bubble Augmented Spline Finite Stripe Method in
Analysis of Continuous Composite Beams. Australian Journal of Structural Engineering.
7(2):75-84.
[9] Vrcelj, Z. e Bradford, M. A., 2009. Inelastic Restrained Distortional Buckling of Continuous
Composite T-beams. Journal of Constructional Steel Research. 65:850-859.
[10] Bradford, M. A. e Gao, Z., 1992. Distortional Buckling Solutions for Continuous Composite
Beams. Journal of Structural Engineering, vol.118:1144.
[11] Bradford, M. A. e Kemp, A. R., 2000. Buckling in Continuous Composite Beams. Progress
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in Structural Engineering and Materials, 2:169:178.
[12] Calado, L. e Santos, J., 2010. Estruturas Mistas de Aço e Betão. IST Press, Lisboa.
[13] Bradford, M. A., 1998. Inelastic buckling of I-beam with continuous elastic tension flange
restraint. Journal of Constructional Steel Research, 48:63-77.