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    Helsinki University of Technology

    Department of Civil and Environmental Engineering

    Rak-83.140 Seminar on Steel Structures

    Zhang Jing 63864F

    Spring 2004

    Design of Composite columns

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    CONTENT

    1. Introduction....................3

    1.1 Types of composite columns....3

    1.2 An example of experiment comparison with steel column..4

    1.3 Advantages of composite columns...5

    2. Composite column design according to Eurocode 45

    2.1 Fundamental design requirements....62.2 Design methods according to EC 4..6

    2.3 The Simplified Method7

    2.3.1 The partial safety factors of materials 7

    2.3.2 Limitations when using the simplified method..7

    2.3.3 Local buckling of steel members. ....9

    2.3.4 Second-order effect..10

    2.3.5 Plastic resistance to axial force11

    2.3.6 Plastic moment of resistance................................................................12

    2.3.7 Resistance to combined compression and bending..13

    2.3.8 Compression and biaxial bending....17

    2.3.9 The influence of shear force.18

    3. Compare with other design codes...19

    3.1 The building code requirements of reinforced concrete (ACI 318-89)..

    19

    3.2 Load and resistance factor design method (AISC-LRFD).20

    3.3 Architectural Institute of Japan (AIJ).20

    3.4 British Standard BS 5400-Part 5....203.5 European Code EC4...21

    4. Reference......21

    Appendix: A Design Example of composite column according to Eurocode4.....

    ..22

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    1. Introduction

    The combination of structural steel and concrete in one bearing system is the basis of

    composite structures. Nowadays the composite slabs, composite beams and compositecolumns are widely used in many countries.

    1.1 Types of composite columns

    A composite column is defined as a compression member which may either be a

    concrete encased section or a concrete filled hollow section. According to the shape of

    the cross-section, there are mainly three different types of composite columns are

    principally in use, see Fig.1.

    Concrete-encased sections (a, b and c) Concrete-filled hollow sections (f, g and i)

    Partly concreted-encased sections (d and e).

    Fig.1 Typical cross-sections of composite column

    Concrete encased columns generally fulfill the technical requirements for high classes

    of fire protection without any additional measures. They can be easily strengthened by

    reinforcing bars in the concrete cover. However, they do not present an accessible

    structural steel surface for later fastenings and attractive surface treatment. This type

    of composite column is the preferred form for seismic-resistant structures. Under

    severe flexural overload, concrete encasement cracks resulting in reduction of

    stiffness while the steel core can continue providing shear capacity and ductile

    resistance to subsequent cycles of overload.

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    Concrete-filled column is used for bridge piers subject to impact from traffic, columns

    to support storage tanks, decks of railways, column in high-rise building and as piles

    for foundations. In concrete-filled hollow sections, the longitudinal reinforcement

    may be not necessary, if design for fire resistance is not required.

    Partly concreted-encased columns have high fire resistance, which is due to that the

    concrete part prevents the inner steel parts - structural steel as well as reinforcing bars

    from heating up too fast. Another significant advantage is that some of the steel

    surfaces remain exposed and can be used for connection to other beams.

    1.2 An Example of Experiment Comparison with steel column

    The basic buckling modes of steel and composite column are illustrated in Fig.2. Inthe case of concrete-filled steel tubular column, concrete inside the tube prevents

    inward-buckling modes of the steel tube wall, and the tube-wall in turn provides

    effective lateral confinement to the concrete inside the tube.

    Fig.2 Buckling modes of steel and composite sections

    Typical example of load-average strain curves for a steel and concrete-filled column

    are shown in Fig.3.

    (a) Steel section (b) Composite section

    Fig.3 Load average strain curves under cyclic loading[1]

    The unloading response of the tubes becomes rapid in case of composite columns,

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    with increasing tube wall slenderness due to local buckling. The response of

    composite tube is similar to that for the bare steel tube. The hysteretic loops in the

    concrete filled column were relatively narrow in early cycles, and then become wider

    at the later cycles due to strain hardening in the post-ultimate region. The maximum

    strength is obtained at about a strain 0f 0.2% in the steel box columns and in the rangeof 0.3-0.4% in the concrete-filled columns. Obviously, the maximum strength of

    concrete-filled columns was much larger than those of the steel columns. Therefore, it

    can be calculated that the concrete-filled column shows good structural performance

    through ductility and high strength.

    1.3 Advantages of composite columns

    There are many advantages associated with the use of composite columns

    (1) High load capacity with small cross-section and economic material use(2) Simple connection to other members, as for steel construction

    (3) Possibility of plastic deformation and ductile behavior

    (4) Good fire resistance

    (5) High resistance to compressive stresses

    (6) Reduced the risk of local buckling of the steel section

    (7) Advantages in fabrication

    For concrete-filled hollow section columns, there are some more special advantages

    (1) Steel is placed in its most effective position at the edge of cross-section

    (2) Concrete works at higher stresses because of the confinement provided by

    the steel tubes

    (3) Fire protection is not usually needed, as the concrete core provides good fire

    resistance

    (4) The steel section serves as formwork during casting

    2. Composite column design according to Eurocode 4

    The Eurocode 4 gives six typical cross-sections of composite columns. See Fig.4.

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    Fig.4 Typical cross-sections of composite columns

    2.1 Fundamental design requirements

    A composite column must be designed for the ultimate limit state. The internal

    stresses and moments resulting from the most unfavorable load combination may at

    no point of the structure exceed the bearing capacity of the cross-section. Effects of

    deformation (p- effects) as well as creeping and shrinkage must be considered if

    they are significant. The influence of residual stresses and initial deformations must

    be considered and reductions of stiffness due to cracking of the concrete in the tensile

    area as well as yield of the steel have to be taken into account.

    Problems due to local and of overall stability must be prevented. Complete bond up to

    failure may be assumed.

    Exact allowance for all these requirements is only possible with complex computer

    programs, which operate non-linearly and incrementally. For practical design,

    simplification must be made so that design can be carried out with minimum effort.

    2.2 Design methods according to EC 4

    Eurocode 4provides two methods for calculation of the resistance of composite

    columns.

    The first is a General Method which takes explicit account of both second-order

    effects and imperfections. This method can in particular be applied to columns of

    asymmetric cross-section as well as to columns whose section varies with height. It

    requires the use of numerical computational tools, and can be considered only if

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    suitable software is available.

    The second is a Simplified Method which makes use of the European buckling curves

    for steel columns, which implicitly take account of imperfections. This method is

    limited in application to composite columns of bisymmetric cross-section which doesnot vary with height.

    These two methods are both based on the following assumptions:

    Plane sections remain plane when the column deforms There is full interaction between the steel and concrete sections until the failure

    occurs

    Geometric imperfections and residual stresses are taken into account in thecalculation, although this is usually done by using an equivalent initial

    out-of-straightness, or member imperfection

    The Simplified Method is discussed in the following part.

    2.3 The Simplified Method

    2.3.1 The partial safety factors of materials

    For the determination of resistance, the following partial safety factors have to be

    applied for the different materials:

    a is the partial safety factor of the structural steel

    s is the partial safety factor of for the reinforcement

    c is the partial safety factor of the concrete

    Thusa

    yyd

    ff

    = is the design value of yield strength of the structural steel

    s

    ssd

    ff

    = is the design value of yield strength of the reinforcement

    c

    c

    cd

    ff

    = is the design value of yield strength of the concrete

    2.3.2 Limitations when using the simplified method

    The scope of this simplified method is limited to members of doubly symmetrical and

    uniform cross-section over the member length. This method is not applicable if the

    component consists of two or more unconnected sections. The following conditions

    should also be fulfilled when use this simplified method.

    (1)The steel contribution ration should fulfill the following condition

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    9.02.0 (1)

    Rdpl

    yda

    N

    fA

    .

    = (2)

    Aa is the cross-section area of the structural steel sectionfyd is the design value for the yield strength of the structural steel

    Npl.Rd is the plastic resistance to compression of the composite cross-section

    (2) The relative slenderness_

    0.2.

    _

    =cr

    Rdpl

    N

    N (3)

    Npl.Rd is the plastic resistance of composite section to compression

    Ncr is the elastic critical normal force for the buckling mode

    b

    eff

    crL

    EIN

    2

    2 )(= (4)

    Lb is the buckling length of the column

    (EI)eff is the effective flexural stiffness of the composite cross-section

    ccmssaaeff IEIEIEEI 6.0)( ++= (5a)

    where Ia, Is and Ic are respectively the second moment of area for structural

    steel section, reinforcing steel section and the uncracked concrete section.

    The coefficient 0.6 for the stiffness of the concrete section takes cracking

    into account.

    The effective flexural stiffness (EI)eff.II of the composite cross-section is used to

    determinate the internal force and second-order effects.

    )5.0(9.0)( . ccmssaaIIeff IEIEIEEI ++= (5b)

    (3) Other limitations

    If the longitudinal reinforcement is considered in design, a minimum percentage of

    0.3% of the reinforcement area must be provided while the maximum percentageshould not exceed 6% of the concrete area.

    For a fully encased steel section, see Fig.5, limits to the minimum and maximum

    thickness of concrete cover that may be used in calculation are:

    hcmm z 3.040

    bcmm y 4.040

    The ratio of the cross-sections depth hc to width bc, see Fig.5, should be within the

    limits 0,2 hc / bc 5.0.

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    Fig.5 Encased sections

    2.3.3 Local buckling of steel members

    For sections completely encased in concrete, local buckling need not be checked.

    The other types of cross-sections must have certain minimum wall thicknesses in

    order to prevent local buckling before reaching the ultimate loads of the system. This

    can be ensured by maintaining a certain limit ratio of depth to thickness of the section.

    Using the notation of Table.1

    Table.1 Maximum values (d/t), (h/t) and max (b/tf) with fy in N/mm2

    Cross-section Max (d/t), max (h/t) and max (b/ tf)

    Circular hollow

    steel sections

    290)(max =d/t

    Rectangular hollow

    steel sections52)(max =h/t

    Partially encased

    I-sections44)(max f =b/t

    accounts for the influence of different yield strengths fy with

    yf/235=

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    2.3.4 Second-order effect

    The influence of second order effects may be neglected in the analysis of bendingmoments for braced and non-sway systems, provided that:

    (1) the normal force NEd is smaller than 10% of the critical load Ncr

    1.0.

    effcr

    Ed

    N

    N(6)

    NEd is the total design normal force

    Ncr.eff is the critical normal force calculated using effective stiffness (EI)eff.II

    (2) the slenderness of the column is

    )2(2.0 r (7)

    r is the ratio of the smaller to the larger end moment(see Fig.6)

    Fig.6 Ration r of the end moment

    If the conditions above are not satisfied, second-order should be taken into account by

    multiplying the maximum first order bending moment by a factor k:

    0.11 .

    =effcrEd NN

    k (8)

    is the equivalent moment factor

    For columns with transverse loading within the column length the value for

    must be taken as 1.0. For pure end moments, can be determined from:

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    44.044.066.0 += r (9)

    2.3.5 Plastic resistance to axial force

    The plastic resistance to axial force is give by Eq.(10), which includes the individual

    resistances of the steel profile, the concrete and the reinforcement.

    For fully or partially concrete-encased steel section:

    sdscdcydaRdpl fAfAfAN ++= 85.0. (10)

    For concrete-filled hollow sections the coefficient 0.85 should be replaced by 1.0.

    This increase is due to the state of tri-axial compressive stresses in concrete resulting

    from the confinement provided by the steel section.

    For composite column with circular hollow sections (CHS), account may be taken of

    increase in strength of concrete caused by confinement provided that the relative

    slenderness does not exceed 0.5 and e/dde

    0.1=a (12e) 0=c (12f)

    For members in pure axial compression, the design value of NEd should satisfy the

    buckling condition

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    0.1.

    Rdpl

    Ed

    N

    N

    (13)

    is the reduction factor, for the relevant buckling mode given in terms of

    the slenderness, column section type and the relevant buckling curve. Eurocode 4has adopted the European buckling curve a, b and c (see Fig.7), which are

    originally established for bare steel column (Eurocode 3)

    Fig.7 European buckling curves according to EC 3

    The factorcan be described mathematically as following:

    0.1)(

    122

    +

    =

    (14)

    ])()2.0(1[5.0 2 ++= (15)

    The factor is used here to allow for imperfections in the cross-sections. Table 2

    gives the value of appropriate for each buckling curve.

    Table 2: Imperfection factor a for the buckling curves according to Eurocode 3

    European buckling curve a b c

    Imperfection factor 0.21 0.34 0.49

    2.3.6 Plastic moment of resistance

    The plastic moment resistance against bending of the cross-section Mpl.Rd may be

    considered to correspond to a full plastic stress distribution according to Fig.8.

    Concrete under tension is neglected.

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    Fig.8 Full plastic stress distribution for a concrete-encased profile

    The determination of Mpl.Rd is explained in the following section.

    2.3.7 Resistance to combined compression and bending

    It is necessary to satisfy the resistance requirements in each of the principal planes,

    taking account of the slenderness, the bending moment diagram and the bending

    resistance in the plane under consideration. The cross-sectional resistance of a

    composite column under axial compression and uniaxial bending is given by an

    interaction curve as shown in Fig. 9.

    0

    Npl.Rd

    Mpl.Rd Mmax.Rd

    Npm.Rd

    0,5 Npm.Rd

    M

    N

    A

    E

    C

    D

    B

    Fig.9 Interaction curve with linear approximation

    The pointD on this interaction curve corresponds to the maximum moment resistanceMmax,Rd that can be achieved by the section. This is greater than Mpl.Rdbecause the

    compressive axial force inhibits tensile cracking of the concrete, thus enhancing its

    flexural resistance.

    The above interaction curve can be determined point by point, by considering

    different plastic neutral axis positions in the principal plane under consideration.

    The concurrent values of moment and axial resistance are then found from the stress

    blocks, together with the two equilibrium equations for moments and axial forces.

    Fig.10 illustrates this process for the example of a concrete-encased section, for four

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    particular positions of the plastic neutral axis corresponding respectively to the points

    A, B, C, D marked on Fig.9.

    Fig.10 Development of stress blocks at different points on the interaction curve

    Point A: Axial compression resistance alone

    RdplA NN .= 0=AM

    Point B: Uniaxial bending resistance alone

    0=BN RdplB MM .=

    Here it can be seen, that in the determination of the resistance of the cross-section,

    concrete regions in tension are taken as being cracked and ineffective

    Point C: Uniaxial bending resistance identical to that at point B, but with non-zero

    resultant axial compression force:

    section)hollowfilled-(concrete

    section)encased-(concrete85.0..

    cdC

    cdCRdpmC

    fA

    fANN

    =

    == (16)

    RdplC MM .= (17)

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    [Note: fcd may be factored by ]1[

    ckf

    yf

    d

    tc+ for a circular concrete-filled hollow section.]

    PointD: Maximum moment resistance

    section)hollowfilled-(concrete5.0

    section)encased-(concrete85.02

    1

    2

    1.

    cdc

    cdcRdpm

    fA

    fANND

    =

    == (18)

    [Note: fcdmay be factored by ]1[

    ckf

    yf

    d

    t

    c+ for a circular concrete-filled hollow section.]

    section)encased-(concrete85.05.0..max cdpcsdpsydpaRdD fWfWfWMM ++==

    (19a)

    section)hollowfilled-(concrete5.0..max cdpcsdpsydpaRdD fWfWfWMM ++==

    (19b)

    Wpa, Wps, and Wpc are the plastic modular respectively of the steel section, the

    reinforcement and the concrete.

    Point E: Situated midway betweenA and C.

    The enhancement of the resistance at point E is little more than that

    given by direct linear interpolation betweenA and C, and the calculation

    can therefore be omitted.

    It is usual to substitute the linearised version AECDB (or the simpler ACDB) shown

    in Fig.9 for the more exact interaction curve, after doing the calculation to determine

    these points.

    We may notice that the stress distribution type C provides the same value for the

    moment of resistance as B, since the moment from the stress resultants in zone 2hn,

    cancel each other. However, the resulting resistance to axial force is of the samemagnitude as the axial force resistance from the pure concrete part Npm.Rd .This can be

    seen from adding up the stress distributions in B and C, with regard to the equilibrium

    of forces, i.e. the resulting axial force. This follows because the resistance to axial

    force in B is zero. Thus, the concrete under compression and that under tensile stress

    are complementary to each other; the stress blocks for the reinforcement provide no

    axial load. A distribution according to Fig.11(a) results. In the same way, subtracting

    the stress distributions of B from that of C analytically produces the stress blocks

    shown in Fig.11(b). The stress resultant in Fig.11(b), only dependent on hn, is

    generally quite simple. The sum of the horizontal force must lead to Npm.Rd. As a

    result an equation for hn, the neutral axis at Mpl.Rd is obtained. This equation is

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    different for various types of section. For example of a concrete encased I-profile with

    bending about the major axis in Fig.11(b), hn is expressed like this

    )2(22

    .

    cdfdwcd

    Rdpm

    nfftbf

    Nh

    += (20)

    Fig.11 Combination of the stress distribution at point B and C considering

    normal force only (a)adding the components; (b) subtracting the components

    Fig.12 shows how the cross-section of a composite column can be checked, by means

    of the interaction curve M-N. The resistance of the column under axial compression is

    defined by the reduction factor . For the factor , a value for the moment k

    representing the moment due to imperfection, can be read off the interaction curve.

    The influence of this moment is assumed to decrease linearly to the value n.

    Fig.12 Design procedure for compression and unaxial bending

    For a normal force

    RdplSdd NN ./= (21)

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    In certain regions of the interaction curve, the normal force increases the moment

    resistance ( > 1.0). If bending moment and normal force are independent of each

    other, the value of must be limited to 1.0. The value n accounts for the fact that

    imperfection and bending moment do not always act together unfavourably.

    For end moments, n may be calculated as:

    =

    4

    1 rn (22)

    r is the ratio of end moments according to Fig.6

    If transverse loads occur within the column length, then n =0, i.e. r = 1.

    The value of moment factor could be obtained from the ineraction curve.

    )(n

    ndkd

    = (23)

    The moment factor represents the remaining moment resistance. It can be shown as:

    RdplSd MM .9.0 (24)

    2.3.8 Compression and biaxial bending

    For the design of a column under compression and biaxial bending the load resistance

    for each axis has to be evaluated separately. It will then be clear which of the axes is

    more likely to fail. The imperfection then needs to be considered for this directiononly (see Fig.13).

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    Fig.13 Verification for compression and biaxial bending

    The combined bending must also be checked using the relative values of moment

    resistance y and z, and a new interaction curve (see Fig.13). This linear interaction

    curve is cut off at 0.9 y and 0.9z; the existing moments My.Sd and Mz.Sd, related to

    the respective resistance, must lie within the new interaction curve. The following

    equations result:

    0.1..

    .

    ..

    . +Rdzplz

    Sdz

    Rdyply

    Sdy

    M

    M

    M

    M

    (25)

    and

    9.0..

    . Rdyply

    Sdy

    M

    M

    (26a) 9.0

    ..

    . Rdzplz

    Sdz

    M

    M

    (26b)

    2.3.9 The influence of transverse shear force

    For simplicity, the design transverse shear force VEd is assumed to be resisted by the

    steel section only. The design shear resistance Vpl.a.Rd of the steel section can be

    calculated as Eq.(27)

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    3/.. ydvRdapl fAV = (27)

    vA is the shear area of the structural steel cross-section

    For RHS profile-if the shear force parallel to the height )/( hbhAA av += (28a)

    -if the shear force parallel to the width )/( hbbAA av += (28b)

    For CHS profile /2 av AA = (28c)

    The influence of transverse shear force on the resistance to bending and normal force

    should be considered ifRdaplEd

    VV..

    5.0> , and a reduced design strength (1-)fyd

    should be used in the shear area Av of the steel section for the determination of

    bending resistance.

    2)1/2( = RdEd VV (29)

    If RdaplEd VV ..> the design shear force VEd may be distributed into the component,

    Va,Ed acting on the structural steel section and Vc,Ed acting on the reinforced concrete

    section.

    Rdpl

    Rdapl

    EdEdaMMVV

    .

    ..

    , > (30) EdaEdEdc VVV ,, > (31)

    Where the plastic moment Mpl.a.Rd and Mpl.Rd refer to the the relevant bending axis.

    The resistance to shear of the concrete part should be verified in accordance with

    Part 1 of Eurocode 2.

    3. Compare with other design codes

    Over the last two decades, researchers have suggested analytical methods and designprocedures for composite columns and design codes have been formulated. Each of

    these codes is written so as to reflect the design philosophies and practices in the

    respective countries. Over the last two decades, different specific codes for the design

    of concreted filled steel tubular column have been used.

    3.1 The building code requirements of reinforced concrete (ACI[2] 318-89)

    According to ACI 318-89, a composite column is a concrete column reinforced with a

    structural steel shape or tubing in addition to reinforcing bars. In order to consider the

    slenderness effects, an equivalent radius if gyration and flexural stiffness are used

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    with a parameter of sustained load ratio, and hence without any sustained load, radius

    of gyration should be taken as zero. The limiting thickness of steel tube to prevent

    local buckling are based on achieving yield stress in a hollow steel tube under

    monotonic axial loading which is not necessary requirement for in-filled composite

    column. A parameter for the softening influence of creep in concrete that is subjectedto sustained compressive loading is included.

    3.2 Load and resistance factor design method (AISC[3]-LRFD)

    This is based on the same principle as ACI code. Design is based on equations for

    steel columns. Nominal strength is estimated on the basis of ultimate resistance to the

    load, and reduction factor are then applied. The nominal axial load capacity is reduced

    according to the slenderness ratio. Neither the ACI-318 nor the AISC-LRFD

    provisions explicitly consider confinement effects on the strength or ductility of

    member analyzed. ACI provisions for calculating the strength interaction betweenaxial and flexural effects are essentially the same as those for reinforced concrete

    column, whereas AISC-LRFD are based on the bilinear interaction formulae which

    have the same form as those of steel columns. In the above design methods, flexural

    stiffness is underestimated and confining effect of the steel tube on the concrete core

    is ignored. The influence of creep is ignored for concrete in composite column

    according to AISC-LRFD specification.

    3.3 Architectural Institute of Japan (AIJ)

    A composite structural system using concrete and steel shape is called steel

    reinforced concrete (SRC) in Japan. The allowable stress design is primarily

    employed, in which working stresses are calculated based on the elastic stiffness of

    members and allowable strength by the superposed strength formulae. Cross-section

    strength is calculated by superimposing the strength of both the steel and concrete

    sections, thereby neglecting the interaction between steel and concrete and the effect

    of confinement. Euler buckling load is used with a reduced concrete stiffness and

    factors of safety for both concrete and steel. The method is applicable to asymmetrical

    sections and column under biaxial bending.

    3.4 British Standard BS 5400-Part 5

    Code provisions in BS 5400 are based on limit state design with loading factors and

    materials safety factors. The ultimate moment is calculated from plastic stress

    distribution over the cross-section, and an approximation for the interaction curve for

    axial load and moment is used. Reduced concrete properties are used to account for

    the effects of creep and the use of uncracked concrete section in stiffness calculation.

    This method is applicable to symmetrical sections only and restricted to the range of

    section catered for in the European buckling curves. It underestimates the capacity of

    in-filled composite column with high-strength concrete.

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    3.5 European Code EC4

    EC4 covers concrete encased and partially encased steel section and concrete filled

    sections with or without reinforcement. This code uses limit state concepts to achieve

    the aims of serviceability and safety by applying partial safety factors to loads andmaterials properties. Based on experimental results, it was recommended that the

    regulations of EC4 concerning the factor of 0.85 should not be applied to hollow

    sections filled with strength concrete. This is the only code that treats the effect of

    long-term loading separately.

    All codes assume full interaction, but some impose restrictions on the shear stress at

    the steel-concrete interface. It is customary to use direct bearing or provide shear

    connectors, if used were the specified limiting shear stress is exceeded.

    4. References

    1. prEN 1994-1-1: Design of composite steel and concrete structures. Part 1-1:

    General rules and rules for buildings. Final draft, 1 January 2002.European

    Committee for Standardization.

    2. prEN 1994-1-2: Design of composite steel and concrete structures. Part 1-2:

    Structural rules-Structural fire design. Final draft, 14 January 2002.European

    Committee for Standardization.

    3. ESDEP Course: WG10:Composite construction. Lecture10.8.1: Composite

    Columns I ; Lecture10.8.1: Composite Columns II

    4. SSEDTA: Structural Steelwork Eurocodes Development of A Trans-national

    Approach. Lecture 8: Composite Columns. @SSEDTA 2001 Last modified

    24/02/04.

    5. Dowling, P. J., Harding, J. E. & Bjorhovde, R.: Constructional Steel Design: an

    international guide. Chapter 4.2 Composite column. Elsevier Applied Science,

    1992.

    6. N.E. Shanmugam & B.Lakshmi: State of the art report on steel-concrete

    composite columns. Journal of Constructional Steel Research, Volume 57, Issue

    10, Pages 1041-1119 (October 2001)7. Aki Vuolio: Design of concreted-filled hollow section columns. (Seminar on steel

    structures, Helsinki University of Technology Laboratory of steel structures)

    [Notes]

    [1]. This figure is based on experiments carried by CFT working group, Japan, 1993. The

    cross-section is circular concrete-filled section, and the load is eccentric, the strength of the

    in-fill concrete is 41Mpa.

    [2]. ACI is the abbreviation ofAmerican Concrete Institute.

    [3]. AISC is the abbreviation of American Institute of Steel Construction.

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    Appendix: A Design Example of composite columnaccording to Eurocode4

    kN 1000 newton:= kNm kN m:= MPaN

    mm2:=

    Structure model and loads see Fig. A

    A composite column pin-supported at both ends , with normal force and bending mome

    about one axis.

    length of the column Lc 10 m:= design value of normal force Nsd 2000 kN:=

    design value of bending moment Msd 100 kNm:=

    Wp.a 966.8 103 mm3:=plasticity modulus

    Ia 13201 104 mm4:=moment inertia

    cross section area Aa 8736 mm2:=

    t 8 mm:=wall thickness

    D 355.6 mm:=diameter of profile

    fyd 3.227 108 Pa=fyd

    fy

    a:=design strength

    a

    1.10:=partical safety factor

    Ea 210000 MPa:=modulus of elasticity

    yield strength fy 355 MPa:=1. Structural steel section

    see Fig. BCross section properties

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    2. Reinforced concrete section

    yield strength of reinforcement(A500HW) fs 500 MPa:=

    modulus of elasticity of reinforcement Es 210000 MPa:=

    s 1.15:=partial safety factor of reinforcement

    es2 91.8 mm:=

    moment of inertia of reinforcement Is 2 As1 es12 2As1 es2

    2+:=

    Is 2.118 105 m4=

    plastic modulus if reinforcement Wp.s 2 As1 es1 2As1 es2+( ):=

    Wp.s 1.969 104 m3=

    compressive strength of concrete (C40/50) fck 40 MPa:=

    secany modulus of elasticity of concrete Ecm 35000 MPa:=

    partial safety factor of concrete c 1.50:=

    fcd

    fck

    c:= fcd 2.667 10

    7 Pa=design strength of concrete

    moment of inertia of concrete Ic D 2 t( )4

    64

    Is:=

    I

    c6.317 10

    4 m4=

    fsd

    fs

    s:= fsd 4.348 10

    8 Pa=design strength of reinforcement

    number and diameter of reinforcing bars ns 8:= s 20 mm:= As1 s

    2

    4:=

    cross section area of reinforcing bars As1

    3.142 104

    m

    2

    =A

    sns

    As1:=

    As 2.513 103 m2=

    Ac D 2 t( )2

    4

    As:=cross section area of concrete

    Ac 0.088m2=

    ration of reinforcement (max value is 6%) s

    As

    Ac

    := s 0.029= s max

    second order effects need to be checked

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    the assumption forAsnis verified

    plastic section modulus of steel and concrete in the region of 2hn

    W

    p.an

    2 t hn

    2:= W

    p.an

    4.132 105 m3=

    Wp.cn D 2 t( ) hn2

    := Wp.cn 8.77 104 m3=

    bending resistance of the cross section with the depth of 2hn

    Mn.Rd Wp.an fyd 0.5 Wp.cn fcd+:= Mn.Rd 2.503 104 J=

    plastic bending resistance (point C and B)

    Mpl.Rd

    MD.Rd

    Mn.Rd

    := Mpl.Rd

    4.57 105 J=

    non_dimensional interaction curve

    NA.Rd Npl.Rd:= NB.Rd 0:=

    1

    2 _2+

    := 0.456= 1.0

    Nsd 2 106 N= Npl.Rd 2.856 10

    6 N=

    Nsd Npl.Rd< OK !

    Resistance to combined compression and bending

    interaction curve piont D

    MD.Rd Wp.a fyd Wp.s fsd+ 0.5 Wp.c fcd+:= MD.Rd 4.82 105 J=

    ND.Rd 0.5Ac fcd:= ND.Rd 1.174 106 N=

    interaction curve point C and B

    NC.Rd 2 ND.Rd:= NC.Rd 1.97 103kN:=

    it is assumed that no reinforcement lies within the region of 2hn

    hn

    NC.Rd

    2 D fcd 4 t 2 fyd fcd( )+:= hn 0.051m=

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    Nsd

    Npl.Rd

    0.319=NC.Rd

    Npl.Rd

    0.315=ND.Rd

    Npl.Rd

    0.188=

    MA.Rd 0:= MB.Rd Mpl.Rd:= MC.Rd Mpl.Rd:=

    MD.RdMpl.Rd

    1.055= Msd_

    Mpl.Rd

    0.301=

    Msd_ is the ampilificated bending moment according to second order effect

    check for utilization ratio of compression and bendin

    moment

    n 1 r( )

    4:= n 0.114=

    dNsd

    Npl.Rd

    := d 0.319=

    drawing the curve of compression and uniaixal bending see Fig.C

    d1 d( )

    1 0.315:= k

    1 ( )

    1 0.315:=

    d kd n( ) n( )

    := 0.517=

    n maxMsd

    0.9 Mpl.Rd

    Nsd

    Npl.Rd,

    := n 0.7=

    0.5 n< 1.0< OK !