simplified method of determination of natural-vibration ... · at the present moment, a suspension...
TRANSCRIPT
Procedia Engineering 57 ( 2013 ) 343 – 352
1877-7058 © 2013 The Authors. Published by Elsevier Ltd. Open access under CC BY-NC-ND license.
Selection and peer-review under responsibility of the Vilnius Gediminas Technical Universitydoi: 10.1016/j.proeng.2013.04.046
11th International Conference on Modern Building Materials, Structures and Techniques, MBMST 2013
Simplified Method of Determination of Natural-Vibration Frequencies
of Prestressed Suspension Bridge
Vadims Goremikinsa,*, Karlis Rocens
b, Dmitrijs Serdjuks
c, Janis Sliseris
d
a,b,c,dInstitute of Structural Engineering and Reconstruction, Riga Technical University, Azenes Str. 16, LV-1048, Riga, Latvia
Abstract
A suspension bridge is the most suitable type for a long-span bridge. Increased kinematic displacements are the major disadvantage of
suspension bridges. This problem can be solved by application of prestressed cable truss.
Dynamic approach is one of regulated bridge design parts. Simplified determination method of natural-vibration frequencies of
prestressed suspension structure and its experimental validation is presented in this paper.
Natural-vibration frequencies and mode shapes of the model depending on the prestressing level were determined. It was experimentally
proved, that mode shape with one half-wave does not appear for the model.
The difference between results, which were calculated by the developed simplified determination method of natural-vibration frequencies
of prestressed suspension structure and experimentally achieved by the model testing, does not exceed 20%. Therefore the method is
applicable for preliminary dynamic analyses of structures.
© 2013 The Authors. Published by Elsevier Ltd.
Selection and peer-review under responsibility of the Vilnius Gediminas Technical University.
Keywords: mode shapes; cable truss; prestressing; natural frequencies.
1. Introduction
Suspension bridges are structures where the deck is continuously supported by the stretched catenary cable [1].
Suspension bridges are the most important and attractive structures possessing a number of technical, economical and
aesthetic advantages [2].
At the present moment, a suspension bridge is the most suitable type of structure for very long-span bridges. Suspension
bridges represent 20 or more of all the longest span bridges in the world. The bridge with the longest centre span of 1991 m
is the Akashi Kaikyo Bridge [3]. So long spans can be achieved because main load carrying cables are subjected to tension
and distribution of normal stresses are close to uniform [4].
Increased deformability is one of the basic disadvantages of suspension bridges [5]. Increased deformability is
conditioned by appearance of elastic and kinematic displacements. The elastic displacements are caused by large tensile
inner forces. The elastic displacements are maximal at the centre of span in case of symmetrical load application. The
kinematic displacements are caused by initial parabolic shape change, resulting from non-symmetrical or local loads [6-7],
see Fig. 1. These displacements are not connected with cable elastic characteristics. Serviceability limit state is dominating
for suspension cable structures.
* Corresponding author.
E-mail address: [email protected]
Available online at www.sciencedirect.com
© 2013 The Authors. Published by Elsevier Ltd. Open access under CC BY-NC-ND license.
Selection and peer-review under responsibility of the Vilnius Gediminas Technical University
344 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
The elastic displacements can be reduced by applying low strength steel structural profiles, elastic modulus increase,
reinforced concrete application and cable camber increase [8].
Fig. 1. Initial shape change under the action of non-symmetrical load Fig. 2. Suspension bridge stabilization by the prestressing
The problem of increased kinematic displacements can be solved by increasing the relation of dead weight to imposed
load, which is achieved by adding of cantledge [9]. However, this method causes the increase of material consumption.
Stiffness of suspension structure can be increased also by increasing of girder stiffness, increasing of main cable camber,
connecting of main cable and girder at the centre of span, application of diagonal suspenders or inclined additional cables,
application of two chain systems, stiff chains and stress ribbons [10-11]. Nevertheless, these systems are characterized also
with material consumption increase, and system stiffness is not sufficient in many cases [12-13].
Usage of prestressed cable trusses is another method of fixing the problem of increased kinematic displacements under
the action of unsymmetrical load [14-15]. Different types of cable trusses are known, such as convex cable trusses, convex-
concave cable trusses, cable trusses with centre compression strut or parallel cable truss [16]. But one of the most efficient
and convenient for application for bridges is concave cable truss [15], see Fig. 2. Cable truss usage allows the development
of bridges with reduced requirements for girder stiffness, but overall bridge rigidity will be ensured by prestressing of
stabilization cable [8]. The deck can be made of light composite materials in this case [17-18].
Dynamic approach is one of the regulated bridge design parts after accident with the Tacoma Narrows Bridge [19-20].
Analyses of natural-vibration frequencies of prestressed suspension structures are realized with labour-intensive discrete
methods at present [21-23]. There is a lack of simple natural-vibration frequency determination methods, which can be used
for approximate design.
The new natural-vibration frequency determination method and its experimental validation are described in this paper.
2. Simplified Method of Determination of Natural-Vibration Frequencies of Prestressed Suspension Structure
For simple suspension bridge simplified equations Eq. (1) and Eq. (2) can be used for mode shapes with odd and even
half-wave number, respectively [10].
6 4 24 4 2 2
, 4 2 2 3
82 c c
v i
c
E A fi EI iH
ml l m i L l m
ππ π ⎛ ⎞ω = + + ⎜ ⎟π⎝ ⎠
, (1)
4 4 2 2
, 4 2v i
i EI iH
ml l m
π πω = +
, (2)
where: i - half-wave number of mode shape;
ωv,i - angular frequency of vertical vibration;
EI - bending stiffness of girder;
l - span;
m - mass of 1 meter of span;
H - horizontal support reaction of main cable; Ec - modulus of elasticity of main cable;
Ac - cross-section area of main cable;
f - camber of main cable;
Lc - length of main cable.
Radicand of the equations Eq. (1) and Eq. (2) can be divided to components: component dependent on girder Eq. (3),
component dependent on support reaction of main cable Eq. (4), component dependent on main cable characteristics
Eq. (5).
345 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
4 4
1 4
i EI
ml
π
α = , (3)
2 2
2 2
iH
l m
π
α = , (4)
6 4 2
3 2 3
82c c
c
E A f
i L l m
π⎛ ⎞α = ⎜ ⎟π⎝ ⎠
. (5)
In comparison with simple suspension bridge, prestressed suspension structure (Fig. 3 and Fig. 4) has additional
stabilization cable, so we can add two additional components for stabilization cable: component dependent on support
reaction of the stabilization cable Eq. (6) and component dependent on the stabilization cable characteristics Eq. (7).
2 2
4 2s
iH
l m
π
α = , (6)
6 4 2, ,
5 2 3,
82 c s c s s
c s
E A f
i L l m
π⎛ ⎞α = ⎜ ⎟π⎝ ⎠
, (7)
where: Hs - horizontal support reaction of stabilization cable;
Ec,s - modulus of elasticity of stabilization cable;
Ac,s - cross-section area of stabilization cable; fs - camber of stabilization cable;
Lc,s - length of stabilization cable.
Fig. 3. Prestressed suspension structure Fig. 4. Cross-section of prestressed suspension structure
Equation of calculation of natural-vibration frequencies of prestressed suspension structure was composed assuming
main and stabilization cables are situated in rows, but left and right cables situated parallel, see Fig. 5.
Fig. 5. Situation of components of prestressed suspension structure
Equations of determination of natural-vibration frequencies for mode shapes with odd half-wave number Eq. (8) and
even half-wave number Eq. (9) were created. These equations allow to calculate natural-vibration frequencies of prestressed
suspension structure.
3 52 4, 1
2 2v i
α +αα +αω = α + + , (8)
2 4, 1
2v i
α +αω = α + . (9)
346 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
3. Experimental Determination of Natural-Vibration Frequencies of Physical Model
3.1. Description of Experimental Model
Physical model was developed to determine natural-vibration frequencies of prestressed suspension structure, see Fig. 6,
Fig. 7). The span of the physical model of the prestressed suspension structure is equal to 2.1 m. Camber of the main cable
is equal to 275 centimetres. The deck is connected to the main cable by suspensions in 15 points. Width of the model is
equal to 0.4 m [24-25].
Fig. 6. Scheme of the physical model of the prestressed suspension
structure
Fig. 7. The physical model of the prestressed suspension bridge
The elements of the model of the prestressed suspension structure are made of steel cables with modulus of elasticity
60000 MPa. Tensile strength of wires of the cables is equal to 1770 MPa. The diameters and cable types of the elements are
shown in Table 1.
Table 1. Characteristics of the Cable Elements of the Physical Model
Elements Cable type Diameter Breaking force
Main cable 6x19+WSC 10.0 mm 63.0 kN
Stabilization
cable 6x19+WSC 8.0 mm 40.3 kN
The deck of the model of prestressed suspension structure is made from oriented strand board (OSB). It does not have
significant load bearing capacity. It only distributes load among suspensions due to deformability of OSB.
The prestressing is organized in the stabilization cables and is developed by rotating of a screw and moving of a bar. The
stabilization cables are supported by the block, see Fig. 8. The tensile force in the stabilization cable was measured by the
electronic dynamometer Scaime IPB50, see Fig. 9. The electronic dynamometer work principle is based on changes of
electrical bridge resistance. The precision of measurements for the electronic dynamometer is 2.5 N [26].
Fig. 8. Prestressing mechanism of the stabilization cable
347 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
Fig. 9. Measurement of prestressing by electronic dynamometer
To connect the deck with the load bearing cable, adjustable suspensions are used, that allow levelling of the deck. The
suspensions are connected to the cables using U-bolt clips [26], see Fig. 10.
Fig. 10. Connection of the deck and main cable by the suspensions
Acceleration sensors were used to obtain natural-vibration frequencies of the model, see Fig. 11.
Fig. 11. Acceleration sensor
The acceleration sensors were situated on the points with numbers 3, 5, 7, 9, 11 and 13 of the model, see Fig. 12 and
Fig. 13. The acceleration sensors measure acceleration at defined time interval with step equal to 0.006255 s and save it to
internal memory. After experiment data can be loaded to PC.
348 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
Fig. 12. Situation of the acceleration sensors on the model
1 2 3 4 5 6 7 8 9 10 11 12 13 14 15
GS1 GS2 GS3 GS4 GS5 GS6
20 kg
Fig. 13. Scheme of situation of the acceleration sensors on the model
Vibration excitation in vertical direction was realized by cutting of suspended weight (20 kg), see Fig. 13. The weight
was connected to the point with number 13 to avoid some mode shape loose. Experiments were done for 6 prestressing
levels: 0, 2, 4, 6, 8 and 10 kN, that correspond to stresses in the stabilization cable equal to 0, 69.7, 139.4, 209.1, 278.7 and
348.4 MPa, respectively.
3.2. Experimental Data Handling
Program ME’scopeVES was used for data handling from the acceleration sensors. The program transforms acceleration-
time dependence into frequency-response function using the Fourier transformation algorithm. Frequency-response function
consists of real and imaginary parts, or magnitude and phase. Natural-vibration frequencies were calculated from
magnitude-frequency dependence. Mode shapes were obtained by connecting imaginary part peaks of each point for each
natural-vibration frequency [27], see Fig. 7.
3.3. Results of the Experiment
Natural-vibration frequencies of the physical model of the prestressed suspension structure were determined depending
on the prestressing level. First three experimentally calculated natural-vibration frequencies in vertical direction are
generalized in Table 2, Table 3 and Table 4, respectively. The first vertical natural-vibration frequency changed from 7.24
to 21.69 Hz, the second frequency changed from 14.55 to 32.61 Hz and the third frequency changed from 21.78 to 40.53
Hz, while the prestressing level changed from 0 to 1000 kg, respectively.
Table 2. 1st Natural-Vibration Frequency in Vertical Direction, Hz
Prestres-sing level P, kN GS 1 GS 2 GS 3 GS 4 GS 5 GS 6 Ave-rage
0 7.18 7.27 7.18 7.33 7.23 7.26 7.24
2 12.37 12.32 12.36 12.35 12.46 12.39 12.38
4 15.26 15.33 15.28 15.40 15.35 15.42 15.34
6 18.18 18.23 18.11 18.11 18.00 18.10 18.12
8 19.95 19.97 20.11 19.92 19.99 20.06 20.00
10 21.71 21.69 21.77 21.56 21.80 21.62 21.69
349 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
Table 3. 2nd Natural-Vibration Frequency in Vertical Direction, Hz
Prestres-sing level P, kN GS 1 GS 2 GS 3 GS 4 GS 5 GS 6 Ave-rage
0 14.56 14.44 14.75 14.87 13.96 14.71 14.55
2 21.14 20.66 21.24 21.12 20.79 21.18 21.02
4 24.63 24.55 24.59 24.85 24.58 24.9 24.68
6 28.19 27.8 28.17 28.17 27.45 28.15 27.99
8 30.42 30.22 30.83 30.38 30.49 30.59 30.49
10 32.61 32.54 32.75 32.44 32.75 32.58 32.61
Table 4. 3rd Natural-Vibration Frequency in Vertical Direction, Hz
Prestres-sing level P, kN GS 1 GS 2 GS 3 GS 4 GS 5 GS 6 Ave-rage
0 21.84 21.41 21.93 22.31 22 21.17 21.78
2 28.62 26.72 26.62 26.79 26.82 27.07 27.11
4 31.61 30.66 30.56 30.79 30.51 30.95 30.85
6 35.75 34.45 34.41 34.51 34.12 34.28 34.59
8 38.4 37.57 37.78 37.72 36.18 37.72 37.56
10 40.59 40.75 40.99 40.6 39.38 40.86 40.53
The dependences between the prestressing level and natural-vibration frequencies, as well as approximation curves are
shown on Fig. 14. The dependence between the natural-vibration frequency and prestression level was evaluated in the form
of second order polynomial.
Fig. 14. Dependence between prestressing level and natural-vibration frequencies
Mode shapes of the first two natural-vibration frequencies in vertical direction are shown on Fig. 15 and Fig 16,
respectively. It was not possible to detect mode shape for third natural-vibration frequency precisely.
As the span of the model was equal to 2100 mm and ends of the girder were not connected to supports, mode shape of
first natural-vibration frequency consists of two half-waves, mode shapes of second and third natural-vibration frequencies
consist of three and four half-waves, respectively. Mode shapes are shown on Fig. 17.
350 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
Fig. 15. Mode shape of 1st natural-vibration frequency
Fig. 16. Mode shape of 2nd natural-vibration frequency
Fig. 17. Mode shapes of natural vibrations of the physical model
Mode shape with one half-wave did not appear for the model. This effect is for the prestressed suspension structure with
small stiffness girder.
4. Validation of Analytical Model
The geometrical and physical parameters of the model of the prestressed suspension structure are generalized in Table 5.
Support reactions of the main and stabilization cables for different prestressing levels were calculated by FEM program
ANSYS and are generalized in Table 6.
Table 5. Geometrical and Physical Parameters of the Model
Parameter of the Physical Model Value
Modulus of elasticity of girder E = 2.3 GPa
Modulus of elasticity of main cable Ec = 60 GPa
Modulus of elasticity of stabilization cable Ec,s = 60 GPa
Girder height h = 0.012 m
Girder width b = 0.4 m
Moment of inertia of girder I = 5.76 · 10-8 m4
Model span l = 2.1 m
Cross-section area of main cable Ac = 4.49 · 10-5 m2
Cross-section area of stabilization cable Ac,s = 2.87 · 10-5 m2
Camber of main cable f = 0.275 m
Camber of stabilization cable fs = 0.174 m
Length of main cable Lc = 2.196 m
Length of stabilization cable Lc,s = 2.138 m
Dead weight of model G = 45.3 kg
Mass of 1 meter of span m = 21.47 kg / m
Natural-vibration frequencies of the model were determined by the developed analytical model according to the
Equations (8) and (9) and are generalized in Table 7. As it was experimentally proved, mode shape of first natural-vibration
frequency of the prestressed suspension structure with small stiffness girder consists of two half-waves.
The differences between analytically and experimentally obtained results are shown in Table 8.
351 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
Table 6. Horizontal Support Reaction Depending on Prestressing Level
Prestressing Level P,
kN Prestressing Level, MPa
Support reaction from
main cable H, kg m/s2
Support reaction from
stabilization cable Hs, kg m/s2
2 69.7 200 112.5
4 139.4 400 205.4
6 209.1 600 295.6
8 278.7 800 383.5
10 348.4 1000 464.9
Table 7. Analytically Determined Natural-Vibration Frequencies of the
Physical Model of the Prestressed Suspension Structure
Prestressing
level P, kN
Number of natural-vibration frequency
1 2 3
Natural frequency ωi, Hz
2 10.7 23.8 32.4
4 13.2 26.5 35.9
6 15.3 28.9 39.1
8 17.2 31.2 42.1
10 18.8 33.2 44.8
Table 8. Comparison of Experimentally and Analytically Determined
Natural-Vibration Frequencies
Prestressing
level P, kN
Number of natural-vibration frequency
1 2 3
Difference between experimentally ant analytically
determined natural-vibrations frequencies, %
2 -15.9 11.5 16.2
4 -16.0 6.8 14.1
6 -18.2 3.2 11.6
8 -16.5 2.1 10.7
10 -15.4 1.8 9.4
The maximum difference between experimentally and analytically determined natural-vibration frequencies does not
exceed 20%, which is enough for design process of structures alternatives.
5. Conclusions
The first vertical natural-vibration frequency of the physical model of the prestressed suspension structure with span
2100 mm changed from 7.24 to 21.69 Hz, the second frequency changed from 14.55 to 32.61 Hz and the third frequency
changed from 21.78 to 40.53 Hz, while prestressing level changed from 0 to 10 kN, respectively.
Mode shape of the first natural-vibration frequency of the model consists of two half-waves, mode shapes of the second
and third natural vibration frequencies consist of three and four half-waves, respectively. Mode shape with one half- wave
does not appear.
Changing of the prestressing level allow to adjust dynamic characteristics of prestressed suspension bridge. Increasing of
prestressing level increases natural-vibration frequency and contra wise. This advantage of prestressed suspension structure
allows improving dynamic characteristics of the bridge and excluding possibility of resonance appearance.
The difference between results, which were calculated by the developed simplified determination method of natural-
vibration frequencies of the prestressed suspension structure and experimentally achieved by the model testing, does not
exceed 20%. Therefore the method is applicable for preliminary dynamic analyses of structures.
Acknowledgements
This work has been supported by the European Social Fund within the project “Support for the implementation of
doctoral studies at Riga Technical University”.
References
[1] Chen, W.F., Lui, E.M., 2005. Handbook of structural engineering. CRC Press LLC, New York, p. 625.
[2] Grigorjeva, T., Juozapaitis, A., Kamaitis, Z., 2010. Static analyses and simplified design of suspension bridges having various rigity of cables, Journal
of Civil Engineering and Management 16(3), pp. 363-371.
[3] Chen, W.F., Duan, L., 2000. Bridge Engineering Handbook. CRC Press LLC, New York, p. 452.
352 Vadims Goremikins et al. / Procedia Engineering 57 ( 2013 ) 343 – 352
[4] Juozapaitis, A., Idnurm, S., Kaklauskas, G., Idnurm, J., Gribniak, V., 2010. Non-linear analysis of suspension bridges with flexible and rigid cables,
Journal of Civil Engineering and Management 16(1), pp. 149-154.
[5] Walther, R., Houriet, B., Isler, W., Moia, P., Klein, J. F., 1999. Cable Stayed Bridges. Second Edition. Thomas Telford, London, p. 236.
[6] Juozapaitis, A., Norkus, A., 2004. Displacement analysis of asymmetrically loaded cable, Journal of Civil Engineering and Management 10(4), pp. 277-
284.
[7] Grigorjeva, T., Juozapaitis, A., Kamaitis, Z., Paeglitis, A., 2010. Finite element modeling for static behavior analysis of suspension bridges with
varying rigidity of main cables, The Baltic Journal of Road and Bridge Engineering 3(3), pp. 121-128.
[8] Kirsanov, M., 1973. Visjachie sistemi povishennoj zhestkosti. Strojizdat, Moscow, p. 116 p. (in Russian).
[9] Strasky, J. 2005. Stress Ribbon and Cable Supported Pedestrian Bridge. Thomas Telford Publishing, London, p. 213.
[10] Bahtin, S., Ovchinnikov I., Inamov R., 1999. Visjachie i vantovie mosti. Saratov State Technical Univeristy, Saratov, p. 124 (in Russian).
[11] Kachurin, V., Bragin, A., Erunov, B., 1971. Proektirovanie visjachih i vantovih mostov. Transport, Moscow, p. 280 (in Russian).
[12] Goremikins, V., Rocens, K., Serdjuks, D., 2012. “Cable Truss Analyses for Suspension Bridge”, Proceedings of 10th International Scientific
Conference, Engineering for Rural Development, 24-25 May, 2012, Jelgava, Latvia. Vol. 11, pp. 228-233.
[13] Goremikins, V., Rocens, K., Serdjuks, D., 2012. “Cable Truss Analyses for Prestressed Suspension Bridge”, in Proceedings of the 8th International
Conference of DAAAM Baltic Industrial Engineering, 19-21 April, 2012, Tallinn, Estonia, pp. 45-50.
[14] Serdjuks, D., Rocens, K., 2004. Decrease the Displacements of a Composite Saddle-Shaped Cable Roof, Mechanics of Composite Materials 40(5), pp.
675-684.
[15] Goremikins, V., Rocens, K., Serdjuks, D., 2011. Rational Structure of Cable Truss, World Academy of Science, Engineering and Technology. Special
Journal Issues 76, pp. 571-578.
[16] Schierle, G. G., 2012. Structure and Design. Cognella, San Diego, p. 624.
[17] Goremikins, V., Rocens, K., Serdjuks, D., 2010. Rational Large Span Structure of Composite Pultrusion Trussed Beam, Scientific Journal of RTU.
Construction Science 11, pp. 26-31.
[18] Goremikins, V., Rocens, K., Serdjuks, D., 2010. “Rational Structure of Composite Trussed Beam”, in Proceedings of the 16th International
Conference, Mechanics of Composite Materials, Riga, Latvia, pp. 75.
[19] Akesson, B., 2008. Understanding Bridge Collapses. Taylor & Francis Group, London, p. 282.
[20] Chen, W.F., Duan, L., 2003. Bridge Engineering. Seismic Design. CRC Press LLC, New York, p. 452.
[21] Almutairi, N. B., Hassan, M. F., Abdel-Rohman, M., Terro M., 2006. Control of Suspension Bridge Nonlinear Vibrations, Journal of Engineering
Mechanics © ASCE June, pp. 659-670.
[22] Bochicchio, I., Giorgi, C., Vuk, E., 2010. Long-Term Damped Dynamics of the Extensible Suspension Bridge, International Journal of Differential
Equations, pp. 1-19.
[23] Bruno, D., Greco, F., Lonetti, P., 2009. A Parametric Study on the Dynamic Behavior of Combined Cable-Stayed and Suspension Bridges under
Moving Loads, International Journal for Computational Methods in Engineering Science and Mechanics 10, pp 243-258.
[24] Goremikins, V., Rocens, K., Serdjuks, D., 2012. Decreasing Displacements of Prestressed Suspension Bridge, Journal of Civil Engineering and
Management 18(6), pp. 858-866.
[25] Goremikins, V., Rocens, K., Serdjuks, D., Gaile, L., 2013. Experimental Determination of Natural Frequencies of Prestressed Suspension Bridge
Model, Scientific Journal of RTU. Construction Science (accepted paper).
[26] Goremikns, V., Rocens, K., Serdjuks, D., 2012. Decreasing of Displacements of Prestressed Cable Truss, World Academy of Science, Engineering
and Technology. Special Journal Issues, 63, pp. 554-562.
[27] Pakzad, S. N., Fenves, G. L., 2009. Statistical Analysis of Vibration Modes of a Suspension Bridge Using Spatially Dense Wireless Sensor Network,
Journal of Structural Engineering © ASCE July, pp.863-872.