Issue Mechanics & Industry Volume 21, Number 5, 2020 Scientific challenges and industrial applications in mechanical engineering 518 9 https://doi.org/10.1051/meca/2020060 13 August 2020

© A. Maati et al., published by EDP Sciences 2020

This is an Open Access article distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/4.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

## 1 Introduction

Sheet metal forming is one of the most important manufacturing processes for mass production in industry. In these processes, plastic deformation is followed by some elastic recovery upon unloading called springback (SB). This complex phenomenon is the geometric change during forming process and it affects the dimensional accuracy of a finished product [1]. SB amount should be taken into consideration so as to produce bent sheet metal parts within acceptable tolerance limits [2]. This phenomenon depends both on process and material parameters such as die radius, sheet thickness, Young's modulus, etc. It has been analysed using different methods over the last few decades. In recent years the FEM is considered as an effective tool to predict SB amount [3]. Various theoretical and numerical models have been proposed to predict SB using tooling geometry and sheet metal properties [46]. Gardiner [7] derived a generalized mathematical analysis for SB correction in the pure bending test. Panthi et al. [8] proposed a phenomenological model for predicting SB in arc bending operation by showing that, the amount of SB is considerably influenced by the geometrical and the material parameters associated with the sheet metal.

Many analytical models proposed to study SB in bending test use simple beam or plate bending theory. These models use simplified assumptions and do not provide error-free predictions [9,10]. Due to the increasingly intrinsic heterogeneous nature of thin metallic sheet, it is of greater interest to introduce heterogeneity parameters into the modelling of the mechanical behaviour [11]. Maati et al. [12] concluded that the results generated by the numerical simulations of SB are more accurate if the material heterogeneities are considered.

Titanium alloys are excellent candidates for aerospace applications owing to their high strength to weight ratio and excellent corrosion resistance [13]. With a density of 4.5 g/cm3, titanium alloys are only about half as heavy as steel or Ni-based super alloys [12]. However, parts made of titanium sheets present more SB compared to parts made of steel. SB occurs because of the elastic relief from the bending moment imparted to the sheet metal during forming [14]. The increase in elastic modulus and in strain hardening exponent leads to a decrease in SB [15]. Due to its highly heterogeneous structure, titanium undergoes large elastic recovery during its formability [12].

In this paper, the 3-point bending test with SB stage was systemically investigated by using numerical simulations. For comparison, two elastoplastic constitutive models are introduced in the finite element code. A comparison with experimental data has been made on strains thanks to the use of digital image correlation.

## 2 Presentation of the two elastoplastic constitutive models

In this study, two different types of phenomenological models were proposed to describe the elastoplastic behaviour of the material. The significant effect of microstructure on SB was studied by using numerical simulations.

### 2.1 Classical modelling

In this case, the material is assumed to be homogeneous and isotropic. In the elastic range, the material behaviour is modelled by Young's modulus and Poisson's ratio. The reference curve between the yield stress and ultimate tensile stress can be described by an elastoplastic model with a von Mises plasticity criterion and isotropic hardening according to Hollomon's law. This later which is a power law relating the true plastic strain to the true stress is given by:(1)

K and n have been identified by fitting the numerical curve to data points. The reference curve will be used as input data in the finite element code.

### 2.2 Hybrid modelling

In this case, the material heterogeneity is considered in the modelling. Different factors determine the degree of material heterogeneity such as phases, subgrain and grain sizes, precipitates and gaps, etc. According to a study carried out by Tabourot et al. [11], materials with hexagonal structure are probably the most heterogeneous relative to other structures (e.g. CFC structure). This property significantly reduces the degree of material homogeneity which causes the dispersion in distribution of strains within the whole volume. One way to account for the heterogeneity is to assign to each element mesh a local behaviour law by using a probability distribution function [17]. The plastic behaviour is described by a bilinear rheological model according to the following relationship:(2)

σy follows a Rayleigh's distribution that requires only one parameter σym, it is comprised between a minimum value σ0 and a saturation value σsat [18]. For the same distribution, nh and σsat are assumed to be constants at any point of the material.

## 3 Experimental tests data

### 3.1 Material characterization

The limits of the chemical composition of the titanium studied are given in Table 1.

Experimental data is of paramount importance in order to obtain reliable and accurate results. To characterize mechanical behaviour of the material studied, various tensile tests are carried out using INSTRON 5569 testing machine fitted with a load cell of 50 kN. These tests are performed on flat samples at a constant crosshead speed V = 7 mm/min. The size of the sample is 70 × 14 × 0.5 (mm3). An extensometer was used to measure the longitudinal strain. The difference between true and engineering stress-strain curves obtained along the rolling direction is illustrated in Figure 1.

In the elastic range, the material behaviour is characterized by Young's modulus (E = 110 GPa) and Poisson's ratio theoretically equal to 0.34 for titanium alloys.

Table 1

Chemical composition limits of the studied material.

 Fig. 1Engineering and true stress–strain curves obtained along the RD.

### 3.2 3-point bending test

To investigate the influence of constitutive model in SB prediction, the 3-point bending test is proposed as a validation test. The device of the test is mounted properly on a tensile testing machine. The sample is placed on 2 supports and then centred on a bending punch. The distance between supports is adjustable (40 mm in our case) as shown in Figure 2. The sample has the same dimensions as that of the tensile test. A speed of 7 mm/min was imposed on the punch to carry out a progressive bending.

The strains of the samples were measured using a digital image analysis. Throughout the test, images were taken every second using a monochrome digital camera (type CMOS EoSens CL) with a resolution of 1280 × 1024 pixels. To have accurately the displacement amount of the punch, a pastille with random speckle pattern of black and white paint was glued to the punch as shown in Figure 3. The different steps of the 3-point bending test are also shown. In this test, the major objective is to evaluate the springback amount after removing the punch.

An area on the speckle pattern was analysed by software 7D [16] as shown in Figure 4. A vertical displacement U2 = 8 mm is imposed to the punch. 7D allows us to obtain multiple output results, for example, Figure 5 depicts the evolution of the punch displacement as a function of time. Perfect agreement is observed between the imposed displacement and the measured displacement using 7D software. Figure 6 gives the diagram of the load applied to the punch on the test piece as a function of the punch displacement. A comparative matching study between measurement data and numerical simulation will be conducted thereafter.

 Fig. 2The 3-point bending device.
 Fig. 3Different steps of a 3-point bending test. (a) Start of the bending test (b) End of the bending test (c) SB stage.
 Fig. 4Digital image analysis. (a) Area analyzed by software 7D. (b) Vertical displacement U2 versus image number.
 Fig. 5Punch displacement as a function of time.
 Fig. 6Diagram force-displacement applied to the punch on the sample.

## 4 Numerical simulation

### 4.1 Identification of the constitutive parameters for both models

The first step of the FE simulation that integrates the material properties is to identify the parameters characterizing both models. These were identified by fitting the numerical curve to experimental data recovered from uniaxiale tensile test. As shown in Figure 7, the values listed in Table 2 give an acceptable agreement between experimental and numerical tensile curves for both types of models. Figure 8, for example, shows the deformation field on the surface of the specimen for both simulations (with and without considering the material heterogeneity).

 Fig. 7Experimental and numerical true stress − strain curves obtained using both types of models.
Table 2

Constitutive parameters for both models.

 Fig. 8Deformation field on the surface of the specimen for both simulations. (a) with classical model. (b) with hybrid model.

### 4.2 Numerical simulation of the 3-point bending test with SB stage

In order to reproduce results from experimental data, a FE simulation was carried out according to the experimental schematic and tooling data previously described. Firstly, a Classical model is considered. The mechanical behaviour of material is initially modelled by the elastic parameters (E and ν) in the elastic range and by a reference curve according to the equation (1) in the plastic range of the tensile curve as shown in Figure 7.

The software Abaqus/Standard was used to setup the numerical model of 3-point bending test with SB stage. The tools were assumed to be perfectly rigid. The part mesh which consisted of 9800 volume elements is obtained using C3D8R element type with 10 elements in the thickness. In order to take the different interactions between the rigid tools and the blank into account, a friction coefficient (µ = 0.15) is proposed. Once the punch has done the prescribed displacement (U 2 = 8 mm), the simulation removes the punch and the SB will occur. For reasons of symmetry, only one-quarter of the test piece need to be modelled.The numerical description of the test is illustrated in Figure 9.

 Fig. 9Numerical description of the 3-point bending test with SB stage.

## 5 Discussion of results

In this work, we proposed and investigated two types of models to describe the elastoplastic behaviour of metals. Subsequently, the proposed models have been used to predict the SB amount in a 3-point bending test. The incidence of material heterogeneity on SB is also discussed by comparing numerical results with experimental measurements. To increase the probability of getting successful results, experimental data were obtained by the image analysis method. As shown in Table 3, the SB value for different methods is presented.

Δx denotes the variation of the maximum deflection of the test piece before and after unloading.

According to the numerical simulation results, an acceptable agreement in terms of SB amount is observed between simulation results based on a random distribution of mechanical properties within the material and experimental data. It has also been observed that the impact of material heterogeneity is less significant in the absence of kinematic hardening as long as the deformation direction is not reversed. This comparison showed an average relative error of less than 10%. Furthermore, this error increases in the case using a conventional approach in which the error is about 13%.

In addition, Figure 10 shows the distribution of the plastic equivalent strain along the selected paths. Path 1 is located in the centre of the test piece.

Figure 11a shows a side view (XY plane) of the test piece just at the end of the loading step. A set of 10 elements is depicted within a small distance dx in the critical zone. As shown in Figure 11b, the material behaviour with classical model is characterized by two specific zones:

• Zone 1: the material behaviour is perfectly elastic, namely that the applied stress tends towards zero after discharge.

• Zone 2: residual stresses are generated after plastic deformation and a tendency to produce a more homogeneous stress distribution within the material. The elements of the set have almost the same elastic-plastic properties; however the final loading states reached are not the same for every element considered in the set.

If the material heterogeneities are introduced in the simulation, the stress distribution is very randomly, i.e. there are even elements not plasticized or relatively plasticized in zone 2. On the other hand, zone 1 may contain relatively plasticized elements. For example, Figure 12 shows the states of stress within the material for the set previously selected.

Table 3

SB values obtained by the different methods.

 Fig. 10Distribution of the plastic equivalent strain using both models. (a) across the sheet thickness (path1) (b) along the length of the sheet (path2).
 Fig. 11State of stress without material heterogeneity. (a) Loading zones (b) Residual stresses in the zone 2.
 Fig. 12States of stress with material heterogeneities. (a) Loading zones. (b) Residual stresses in the zone 2 (random distribution).

## 6 Conclusion and perspective

In this paper, two elastoplastic constitutive models have been proposed to characterize the elastoplastic behaviour of the studied material. The first is a classical model which assumes that the material properties are homogeneous within the whole volume of the sample, while the second is a hybrid model in which spatial heterogeneities are introduced using Rayleigh's distribution of hardening parameters. Then both were implemented into a finite element code which was used to predict SB for 3-point bending test. An experimental characterization of the material response using titanium sheets was performed in order to obtain the reference curve that will be used as input data in the FE code. A python script coupled to Abaqus is used to establish the identification of hardening parameters of both models. An acceptable convergence is observed between the numerical results using bilinear approach as a local law and the experimental measurement of SB, the error increases if the material heterogeneity is not included. Fine optimization of hardening parameters can effectively improve the numerical results.

Finally, this type of physically based models will certainly be more effective to predict complex phenomena generated by the plastic deformation and which are more sensitive to the material heterogeneities such as the strain localization and kinematic hardening. It will be soon tested for complex path of deformation to check the potential of such a model.

The investigation of the effects of other parameters (type of mesh, choice of distribution function and local law, etc.) is still underway.

## Nomenclature

nh (MPa): Hardening rate

σy (MPa): Threshold stress

σym (MPa): Average yield stress

σsat (MPa): Saturation stress

Δx (mm): Springback amount

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Cite this article as: A. Maati, L. Tabourot, P. Balland, S. Belaid, Influence of the material microstructural properties on a 3-point bending test, Mechanics & Industry 21, 518 (2020)

## All Tables

Table 1

Chemical composition limits of the studied material.

Table 2

Constitutive parameters for both models.

Table 3

SB values obtained by the different methods.

## All Figures

 Fig. 1Engineering and true stress–strain curves obtained along the RD. In the text
 Fig. 2The 3-point bending device. In the text
 Fig. 3Different steps of a 3-point bending test. (a) Start of the bending test (b) End of the bending test (c) SB stage. In the text
 Fig. 4Digital image analysis. (a) Area analyzed by software 7D. (b) Vertical displacement U2 versus image number. In the text
 Fig. 5Punch displacement as a function of time. In the text
 Fig. 6Diagram force-displacement applied to the punch on the sample. In the text
 Fig. 7Experimental and numerical true stress − strain curves obtained using both types of models. In the text
 Fig. 8Deformation field on the surface of the specimen for both simulations. (a) with classical model. (b) with hybrid model. In the text
 Fig. 9Numerical description of the 3-point bending test with SB stage. In the text
 Fig. 10Distribution of the plastic equivalent strain using both models. (a) across the sheet thickness (path1) (b) along the length of the sheet (path2). In the text
 Fig. 11State of stress without material heterogeneity. (a) Loading zones (b) Residual stresses in the zone 2. In the text
 Fig. 12States of stress with material heterogeneities. (a) Loading zones. (b) Residual stresses in the zone 2 (random distribution). In the text

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