Effect of Spun Velocities and Composition on the R‒phase and Thermomechanical Behavior in Ti‒Ni Ribbons Electrically Heated

Abstract

This work deals with structural, electrical and mechanical characterization of Ti‒50.13Ni and Ti‒49.62Ni (at.%) shape memory alloys (SMAs) fabricated at different circumferential wheel velocities. The effect of wheel velocity, chemical composition and heat treatments are investigated. The characterization of crystallographic phases of the Ti‒Ni ribbons was carried out using X-ray diffraction. Electrical resistance variations as function of temperature (∆R/R %) were analyzed using a non-commercial technique, which consists in a thermal-adjustable bath apparatus revealing the temperatures of B2→R→B19´ two stage transformation, whereby the presence of R‒phase can be definitively confirmed. The Stress-Assisted Two-Way Memory Effect was measured by an own designed apparatus with an Linear Variable Differential Transformer captor and a current controlled heating, and results indicate that the as-spun condition, promotes the Stress-Assisted Two-Way Memory Effect. On the other hand, increments in Ni content tend to decrease transformation temperatures and high wheel velocities help to the R‒phase formation.

Keywords:  Ti‒Ni Ribbons; Melt-spinning; R‒phase; Electrical Resistance; Joule Effect; Shape Memory Alloys

1 Introduction

Near equiatomic Ti‒Ni shape memory alloys (SMAs) are well known to exhibit a thermoelastic martensitic transformation associated to B2 to R‒phase and B19´, with superelastic (SE) and a shape memory effect (SME) ^1–4. In these SMAs, the R‒phase martensitic transformation is known to precede the B2→B19´ martensitic transformation under certain conditions, as thermal cycling and thermomechanical treatments mainly. The existence of the R‒phase depends on several factors like composition, thermal history cycling, degree of cold work and solution treatment of the sample. In most cases the R‒phase is not very pronounced and several thermal cycles are required to make it appear more clearly⁵.

Widespread results of SME have shown in the literature, a simple step transformation related to the B2→B19´sequence (as in Ti‒Ni, Ti‒Ni‒Cu₅ alloys), however in some cases, as in Ti‒Ni alloys, two peaks of martensitic transformations in DSC curves could be favored (B2→R→B19´) basically in three ways: by cold work, by ageing of the alloys with higher Ni content, and by the addition of a third element e.g. Fe. Other results have proven that the position of the peaks according to the temperature could be affected by thermal and thermomechanical cycling and heat treatments, causing an increase of the temperature of the peak of B2 and an overlapping of both peaks in DSC, even some authors have reported that R‒phase transformation could disappear ^6,7-9. When this overlapping of phases takes place, techniques as electrical resistivity variation has greatly helped to identify the R-phase and the sequence of transformation can be followed ^10-11. Electrical resistivity variations of SMA during thermal or mechanical tests have been investigated for a long time, showing that these variations are considered to depend mainly on the volume fractions of the austenite and martensite phases. In addition to this, measurements of electrical resistance (ER) with temperature have commonly been used to evaluate transformation temperatures of SMAs^12-13.

On the other hand, R‒phase martensitic transformations in Ti‒Ni SMA are known to be attractive for its small transformation hysteresis, high stability during thermomechanical cycling and superior functional fatigue resistance. Some authors have suggested methods as melt-spinning for inducing the B2→R martensitic transformation^14-15. Moreover, it is known that mechanical properties as Stress-Assisted Two-Way Memory Effect (SATWME) in Ti‒Ni alloys are very important for the development of smart actuators manufactured from this special kind of non-conventional material⁷. However, R-phase transformation is not fully beneficial for those applications where a position control is required (e.g. actuators) ^4-5,14,16-20.

Based on aforementioned backgrounds, the objectives of this paper are: to determine the influence of the cooper wheel velocity, heat treatment and chemical composition over the thermal and electrical behavior of the ribbons, and to estimate which conditions are the more interesting for possible applications in the field of micro-actuators or micro-robotics, taking into account only the SATWME of the ribbons electrically heated, which could be a normal situation in the field of actuators. In addition to this, to investigate the electric resistance behavior of Ti‒Ni ribbons presenting the R‒phase transformation.

2 Experimental Section

The conventional vacuum induction melting (VIM) process was employed to elaborate binary Ti‒Ni SMAs. Two buttons were fabricated by VIM with nominal composition of Ti‒50.13Ni and Ti‒49.62Ni (at.%) and were called M1 and M2, respectively. It is important to mention that elements used for this investigation have high purity (Grade 1 Ti, 99.80 wt.% and electrolytic Ni, 99.95 wt.%). Their transformation temperatures obtained by DSC are presented in table 1 ^21-22. After that, the buttons were placed in a melt-spun equipment to produce ribbons.

Table 1
Phase transformation temperatures of the row materials^a.

Alloy	As (°C)	Af (°C)	Ms (°C)	Mf (°C)
M1	58.0	77.9	49.7	34.9
M2	67.6	87.8	59.3	44.0

• ^a
  Grade 1 Ti, 99.80 wt.% purity (balance); electrolytic Ni, 99.95 wt.% purity.

The melt-spun ribbons were produced under a 200 mbar argon atmosphere using a quartz crucible with a nozzle diameter of 1.0mm; the melt was ejected onto the surface of a polished copper wheel having a tangential wheel speed fixed at 30, 40 and 50 m/s. The distance between the nozzle and the copper wheel was 0.5 mm. The thickness average of the ribbons varied from 30 up to 50 μm, where those with lower thickness and lower width were the ribbons produced at 50 m/s ²³. With the aim to homogenize the microstructure and decrease defects like dislocations generated during melt spinning, samples were heat treated at 350°C during 1 and 5 hours. Table 2 gives some characteristics of the obtained ribbons, focusing on the chemical composition which was measured by energy dispersive x-ray (EDX) in order to corroborate the composition initially used in the VIM process to obtain the buttons M1 and M2. As can be seen, EDX results are very close to the initial composition, proving that M1 is rich in Ni and M2 in Ti, even the 95% of EDX accuracy.

Table 2
Thermal and chemical characteristics of the obtained ribbons

Alloys	Tangential Wheel Speed, m/s	HT‒1	EDX			HT‒2	EDX
			Ti (at %)		Ni (at %)		Ti (at %)	Ni (at %)
M1 Ti‒50.13 at. % Ni	30 40 50	350°C‒1h	49.7 49.5 49.1	50.3 50.5 50.9		350°C 5h	49.3 49.7 49.7	50.7 50.3 50.3
M2 Ti‒49.62 at. % Ni	30 40 50	350°C‒1h	50.6 50.3 50.4	49.4 49.7 49.6		350°C 5h	51.0 51.7 50.2	49.0 48.3 49.8

Crystallographic planes and phases were investigated by X-ray Diffraction (XRD) using CuKα radiation (Bruker Advanced X-ray Solutions D8) at a rate of 6.0 °/min. ER measurements using the four wires ohms method were carried out in a thermal-adjustable bath containing silicone oil for thermal cycling with a calibrated K type thermocouple to measure the temperature. The accuracy in temperature measurement is around ±1.1°C to 2.2°C. The measurement system is also equipped with a controlled power supply to maintain a constant electrical current in the ribbons and a data acquisition device (Agilent, model 34970A) for storage the voltage drop during thermal cycling. The temperature range was configured from 90°C to -10°C in order to study the range were the martensitic transformation takes place. The Ti‒Ni ribbons were connected in series to undertake five measurements in one run. The employed electrical current was of the order of 400 mA, causing an initial voltage drop of about 600 mV on each ribbon ²⁴. Finally, to study the SATWME under constant load, thermomechanical cycles between the Austenite (A) and Martensite (M) phases were carried out using an apparatus developed in our laboratory through a special program, which is connected to a Linear Variable Differential Transformer (LVDT) device for measuring small displacements. The sample is held with jaws attached to a pulley system with a constant load. When the electric current passes through the sample, the ribbon is heated and transformed into austenite, the cycle is completed by cooling in air at room temperature by removing the current slowly. Furthermore, the strain at high and low temperature is measured with the LVDT. Data acquisition of electrical current and deformation is computer controlled, and is possible to construct a curve of strain vs. current density. Then, the SATWME could be obtained from the difference between the strain of the phases at low and high temperature.

3 Results and Discussion

3.1 XRD results of the as-spun melted and heat treated Ti‒Ni SMA ribbons

In order to study the phases presented in the Ti‒Ni SMA ribbons, X-ray diffractions were performed at room temperature and results are show in figure 1. These patterns consist on peaks corresponding to the martensite phase B19´ with a monoclinic structure which suggests that Ms is above room temperature for all cases. However, in other states, some peaks correspond to the austenite phase B2 with a cubic structure are also present, as well as, R‒phase which possess a rhombohedral structure. For those cases it can be inferred that Mf is below room temperature. Moreover, R‒phase is favored as defects are promoted. This is exactly what is happening in the ribbons of the as-spun state of M1 and M2 (figure 1a-b), it can be seen that at lowest tangential wheel speed of 30 m/s, only peaks corresponding to B19´appears, because this is the condition that should present larger grain size and higher Mf¹, as it was previously reported by Nuñez Mendoza ²⁵. In the XRD patterns of M1 at 40 and 50 m/s small diffraction peaks corresponding to the B2 phase and R‒phase start to appear at 42.37°, 43.18° and 61.53° respectively, corresponding to the planes B2 (110), R (11$\overline{2}$) and R (22$\overline{2}$) and it can be said that Mf temperatures decreased with wheel speed increasing, which can promote the presence of R‒phase and B2 at room temperature in XRD patterns. For M2 Ti-rich alloy, the increasing of the wheel speed defects should be the cause that promotes the development of the R‒phase. Now, the apparition of all the phases (B2, R and B19´) in the other XRD patterns for all the heat treated samples from figure c-f, is explained because the Mf for these ribbons is lower than the Mf for the ribbons as-spun conditions. Moreover, the peak at 61.53° corresponding to the R-phase shows an increase in almost all states of the M1 compared with peaks of M2, which confirm that the Ni promotes the presence of the R-phase. With the only exception of XRD pattern of the HT1-M1 at 40 m/s, it can be appreciated that peaks of the B19’ phase are lightly higher when the temperature or the time of the HT increases. This suggests that with higher HT in temperature and time, less defects and more transformed martensite at room temperature should be expected, and possibly the R-phase could disappear.

Figure 1
X-ray diffraction analyses of Ti−Ni ribbons of (a-b) as-spun, (c-d) M1 with HT-1 and HT-2, (e-f) M2 with HT-1 and HT-2, respectively.

3.2 ER variations of Ti‒Ni shape memory alloy ribbons

Figure 2 shows the curves of ER variation (ΔR/R) as a function of temperature for analyzed Ti‒Ni ribbons described in table 2 at 30 m/s and 50 m/s. As expected, in comparison between Ti‒Ni and Ti‒Ni‒Cu SMAs, the curves do not exhibit the typical forward and reverse “S” shape of classical martensitic transformations of SMAs, as it was demonstrated recently by De Araújo et al.²⁶. This is due because the R-phase of samples M1 and M2, causes an abrupt augmentation of the electrical resistance of the material, while by adding Cu at around 5%, the R-phase disappears and this promotes curves with the “S” shape in the electrical behavior during termomechanical tests at constant stress ²⁶.

Figure 2
Dependence of the electrical resistance versus temperature curves corresponding to the (a-b) as-spun M1 and M2, (c-d) M1 with HT-1 and HT-2, (e-f) M2 with HT-1 and HT-2, respectively; in a complete thermal cycle.

From literature, a rapid increase in electrical resistance while cooling is associated to R‒phase formation²⁷. It has been reported that the appearance of R‒phase on Ti‒Ni is due to the increase in Ni content, thermal cycling and aging. Besides, the microstructural defects produced during the melt-spinning at high speed enhance the formation of R‒phase ²⁸, which corroborates the results obtained in figure 2. The appearance of martensitic R‒phase is characterized by the high increase in ER (Electrical Resistance) and then a decrease when B19´martensitic phase appears ²⁹. The results show that higher variation of ER was observed by those heat-treated ribbons, meaning that more R‒phase is developed, which is in agreement with XRD results. It can be noted that for ribbons of M1 and M2 as-spun melted state (figure 2a-b), curves show undefined phase changes during cooling with small percentage of ER variation in the sequence B2→R→B19´martensic transformation. This fact is also in agreement with results of XRD presented in figure 1, where, as-spun ribbons only show small signs of R‒phase, and the fact that materials with no heat treatment normally present a heterogeneous microstructure, was solved applying heat treatments (HT‒1 and HT‒2) resulting well-defined curves as shown in figure 2c-f, where there is a clear increment in the ΔR/R axis during B2→R transformation, and then a dramatic decrease of ΔR/R during R→B19´. These results are opposite to those expected about that dislocations promote the R-phase and that higher heat treatments should decrease defects and also R-phase. But results seems to indicate that this two HT in the M1 and M2 ribbons, allow an increase in the amount of transformation because in the as-spun ribbons, the transformation is strongly blocked, and this could be the reason of this increase, not only of the R-phase but also of the martensite phase. In this sense, as perspective in a future work, higher HTs must be done in order to elucidate this point, because authors have suggested that higher and longer heat treatments are needed to suppress de R-phase ⁷. On other hand, while cooling, the ER increased suddenly at Rs, reached the maximum ∆R/R value at Ms. On other hand, as can be seen ribbons annealed at HT‒2 show the maximum ER variation for the most cases, giving more than 13%, in relation with the B2 austenite parent phase.

Although others characterization techniques like DSC or XRD can show a slight evidence of R‒phase, this phenomenon could not be completely followed. Contrary, as it is shown in figures 2a to 2f, at less for ribbons Ti‒Ni with this chemical composition and heat treatments, the use of techniques as 4-wires method (adapted to this non-commercial apparatus developed by Lima et al., ²⁴) is helpful to study all the kinetic of transformation of R‒phase while the temperature is changing. Analyzing now those ribbons subjected at HT‒1 and HT‒2 some issues can be mentioned. It is remarkable that a longer heat treatment tends to stabilize TTRs for the M1 and M2 regardless the wheel speed. Then, Ti‒Ni ribbons examined in this work can be used as high precision devices in a width range of temperatures.

3.3 Recovery strain response of Ti‒Ni ribbons

Coupled measures of memory effects and physical properties are of interest in the study of the martensitic transformation, and the mutual relationship can be used to control SMA actuators. Moreover, this work could be very interesting from the point of view of applications because of the way of characterizing the SATWME activated by Joule effect (electrical heating), which could be a very normal situation of application in SMA actuators, like in an interrupter On/Off or a valve. In this work, experimental results recorded in electrical density cycles at several constant stresses are shown in figure 3 only for the most interesting states from the mechanical point of view, the M2 as-spun and M2 at HT‒1 at 50 m/s. The ribbons were loaded to a desired stress level in the austenitic state at T>Af, then they were cooled down below the T<Mf temperature under stress, and subsequently heated by Joule effect back to austenite phase above the Af temperature. After one cycle, the stress was increased and a new cycle was carried out. In figure 3a the strain variation in function of the current density across the transformation range under different constant loads are showed for a ribbon as spun condition. In this same figure is indicated the way to measure the SATWME and the plastic strain (ε_P) which are plotted in the figure 3b. A small load (close to zero marked as P) was necessary in order to start the test with the ribbons completely straight. At around 0 MPa (figure 3b) an important strain recovery of almost 2% can be observed, which can be related to a reorientation of martensite variants during the melt spinning process in the direction of the wheel rotation. This phenomenon has been previously observed during cold drawing ³⁰ and cold rolling ³¹, the TiNi base alloy has shown a strong variant anisotropy in the direction of the fabrication process, this can be easily observed because these samples show a strain recovery without any applied stress after the elaboration process and a heat treatment, i.e. in curves of strain vs. temperature at 0 MPa, they present a strain or a displacement in the direction of the process, which is actually a Two Way Memory Effect (TWME). Then in the figure 3b, it can be observed that the SATWME increases with the stress, but very soon, at around 70 MPa, the SATWME reaches its stability, and after 240 MPa an apparent loose of SATWME seems to take place. On the other hand, the plastic strain ε_p increases lineally with the stress and the R-phase is observed at the beginning of almost all the curves.

Figure 3
Strain-Current Density during thermal cycles under different constant stresses for M2 ribbons processed at 50 m/s, a) as-spun, c) annealed at HT-1, b) and d) show SATWME (open symbols) versus plastic deformation (filled symbols) for as-spun and annealed respectively

Now if the sample is heat treated at 350 °C during 1 hour (figure 3 c and d), a small strain recovery of 0.4% at around 0 MPa, is observed. This means that the effect of the reorientation of martensite variants during the melt spinning process described above, is almost lost. Consequently the SATWME is also affected; there is also a diminution of the maximum SATWME with only 3%, and the stability is reached until 180 MPa. The plastic strain ε_p also increases lineally with the stress but the R-phase is not clearly developed as for the as-spun condition. These results indicate that the heat treatment process at 350°C-1h (HT‒1), is not entirely beneficial, because annealed ribbons show lower values of SATWME , and the strain recovery close to 0 MPa induced by the spun process and also the good stability were lost. Then, heat treatments of lower temperature or with less time of duration must be studied in future works. Moreover studies with TiNiCu ribbons are suggested to be explored with same conditions, in order to avoid the R‒phase.

As it was mentioned by Wada and Liu ³², there is a strong relation between the increase in SATWME and the increase in plastic strain (ε_P), and this can be explained from the viewpoint of a work-hardening effect attributed to the increase in dislocation density; thermomechanical cycling and stress at the initial stage causes a rapid increase in dislocation density, but then after cycling is more difficult to develop. Furthermore, during the thermomechanical cycles, a dislocation network has been developed that was most favorable to the internal stress field ³³, which in turn causes the martensite variants to be aligned in preferential orientation, making it possible to develop the SATWME. In this work, these results of accumulated cycles seem to indicate that the best compromise between aligned martensite variants (SATWME) or full utilization of the martensite reorientation capacity and dislocation density for M2 as spun, will take place between the 85 and 150 MPa and for the M2 with HT1 between 180 and 240 MPa.

4 Conclusions

All states, including the as-spun ribbons obtained by melt spinning process, present the reversible austenite ↔ martensite transformation, validating this process for elaborating equiatomic NiTi ribbons. Ribbons processed by this method did not exhibit the typical forward and reverse “S” shape of classical martensitic transformation of SMAs, opening the possibility to use these ribbons with small transformation hysteresis (B2→R), if a small recovery of strain is desirable. Chemical composition had an important role in the thermal and electrical behavior of quasi-equiatomic TiNi SAMs. It has been demonstrated in this work that variations on any of these elements, affect the transformation temperature, e.g. an increase in the NiTi content, tends to decrease the M_s temperature and more R-phase is detected. On the other hand, the increase in the spun velocity, promotes the presence of R‒phase. Then, the obtained results indicate that the combination of higher spun velocity with Ni-rich alloy should be desirable if R‒phase is wanted. Results obtained from SATWME curves indicate that, orientation of martensite variants under load is a process that can be activated even at very low stress levels, reaching values of strain recovery close to 3.7%, an important value for microactuators applications. Heat treatment after as spun condition is not entirely beneficial for spun ribbons, because annealed ribbons show lower values of SATWME. The ER apparatus used in this work, can be proposed for measuring electrical resistance variations in function of temperature, being good and effective alternative in the detection of phases present in alloys which show martensitic transformation. Finally, the developed Apparatus of Thermomechanical cycles to study SATWME, is a good alternative to characterize SMAs ribbons, and the results of Strain vs Current Density can be used directly to predict the expected mechanical behavior in a actuator activated by Joule Effect. Moreover, other geometries could be analyzed in this equipment, such as wires and small bars.

Acknowledgments

Authors wish to thank to the CONACYT and CIAM for their financial support from the 82515 and 107462 projects. This work was technical supported by FIME-Universidad Autónoma de Nuevo León (UANL), Centro de Innovación, Investigación y Desarrollo en Ingeniería y Tecnología (CIIDIT), Multidisciplinary Laboratory on Active Materials and Structures, Department of Mechanical Engineering, Universidade Federal de Campina Grande, Brazil and Technological Institute of Aeronautics, São José dos Campos, SP, Brazil.

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Publication Dates

• Publication in this collection
  May-Jun 2016

History

• Received
  13 Jan 2016
• Accepted
  07 Mar 2016