Patent Document

CROSS-REFERENCE TO RELATED APPLICATIONS 
     This application is based upon U.S. Provisional Application Ser. No. 60/129,486 filed on Apr. 15, 1999, from which the benefit of priority pursuant to 35 USC § 120 is hereby claimed, and the full content which is incorporated herein by references as though fully set forth. 
    
    
     BACKGROUND OF THE INVENTION 
     1. Field of the Invention 
     The present invention relates generally to micro-actuators, and particularly to switching of micromirrors in microelectromechanical systems (MEMS). 
     2. Technical Background 
     Micromechanical actuators are essential for microelectromechanical systems (MEMS) that require movable components. For applications such as a free-space optical fiber switch or for self-assembly of a three-dimensional MEMS structure, a compact actuator with long-range fast-speed traveling ability is often necessary. Known actuators have mechanical power transmission mechanisms based on an electrostatic driving element, such as scratch drive actuators, resonator-based vibromotors, microengines and stepper motors. Most of the devices, however, require not only large areas (&gt;1 mm 2 ) but also large driving voltages (10&#39;s of volts to more than 100 volts). Moreover, either two sets of actuators or complicated phase-matching operation is required for the actuators to have a two-direction actuation capability. As multiple devices are needed on a chip, the actuators desired need to occupy a sufficiently small space and be driven using low voltages. It is further desired to be able to change the direction of the actuator by simply adjusting the applied electrical current, in order to save space and simplify the power supply design of the MEMS 
    
    
     BRIEF DESCRIPTION OF THE DRAWINGS 
     FIG. 1 is a top view representation of an electrothermal vibromotor, in accordance with the present invention. 
     FIG. 2 is a top view representation of the thermal actuator  20  of FIG. 1, in accordance with the present invention. 
     FIG. 3 is a top view depiction of the motion sequence of the thermal actuator  20  of FIG. 1, in accordance with the present invention. 
     FIG. 4 is a microscopic photograph of the slope-shaped impact head  40  of the thermal actuator  20  of FIG. 2, in accordance with the present invention. The inserted picture shows the rounded head design separated from the thick arm of the actuator to show the driving mechanism more clearly. 
     FIG. 5 a  is a chart showing the current square (I 2 ) vs. time (t) plot of the sinusoidal AC voltage input at low frequency. 
     FIG. 5 b  is a chart showing the current square (I 2 ) vs. time (t) plot of the sinusoidal AC input at high frequency 
     FIG. 5 c  is a chart showing the current vs. time plot of the AC+DC input, in accordance with the present invention. 
     FIG. 5 d  is a chart showing the current square (I 2 ) vs. time (t) plot of the AC+DC input, in accordance with the present invention. 
     FIG. 6 is a chart showing the measured system driving current vs. frequency based on a sample of six thermal actuators in two operational modes. 
     FIG. 7 is a scanning electron microscope (SEM) photograph of a fiber optic switch with an integrated electrothermal vibromotor, in accordance with the present invention. 
     FIG. 8 is a top view depiction of the motion sequence of the thermal actuator  20  of FIG. 1, showing more detail of the two operation modes in the same swing cycle, in accordance with the present invention. 
     FIG. 9 is a perspective view representation of the electrothermal vibromotor  10  of FIG. 1, in accordance with the present invention. 
    
    
     DETAILED DESCRIPTION OF THE PREFERRED EMBODIMENTS 
     Additional features and advantages of the invention will be set forth in the detailed description which follows, and in part will be readily apparent to those skilled in the art from that description or recognized by practicing the invention as described herein, including the detailed description which follows, the claims, as well as the appended drawings. 
     It is to be understood that both the foregoing general description and the following detailed description are merely exemplary of the invention, and are intended to provide an overview or framework for understanding the nature and character of the invention as it is claimed. The accompanying drawings are included to provide a further understanding of the invention, and are incorporated in and constitute a part of this specification. The drawings illustrate various embodiments of the invention, and together with the description serve to explain the principles and operation of the invention. 
     A polysilicon surface-micromachined electrothermal vibromotor (ETV motor) that is capable of long travel ranges, high speeds and simple directional control is taught by the present invention. With features like integrated circuit compatible driving voltages, and very small footprint, it is especially suitable for systems requiring a high-density of actuated devices on a silicon chip. The electrothermal-based vibromotor, taught by the present invention, occupies a space smaller than 200×300μm 2  and is driven using CMOS integrated circuit compatible voltages. Furthermore, the direction of the vibromotor can be changed by simply adjusting the applied electrical current, greatly simplifying the power supply design of the fiber optic switch system. Optimization of the power consumption and speed of the linear vibromotor can be made using different materials and through better thermomechanical design of the thermal actuator. 
     It is known that vibromotors rely on impact actuation to obtain relatively large armature movement from small-displacement vibrating elements. The present invention teaches a different method and apparatus to provide the impact actuation. A representation of an electrothermal linear vibromotor including vibrating thermal elements that drive a guided slider or any other movable guided element through oblique impact is shown in FIG.  1  and FIG.  9 . 
     Reference will now be made in detail to the present preferred embodiments of the invention, examples of which are illustrated in the accompanying drawings. Wherever possible, the same reference numbers will be used throughout the drawings to refer to the same or like parts. An exemplary embodiment of an apparatus of the present invention is the vibromotor of the present invention as shown in FIG.  1  and FIG. 9, and is designated generally throughout by reference numeral  10 . 
     Referring to FIG. 1, an apparatus  10  to provide impact actuation in a microelectromechanical system (MEMS) includes an electrothermal linear vibromotor having at least one vibrating thermal element  20  pivotally attached for providing oblique impact actuation. A movable guided element  10  is slidable in response to the oblique impact actuation of the electrothermal linear vibromotor. 
     The vibrating elements are thermal actuators  20  of FIG. 2 that are positioned at 45 degrees on both sides of a slider  110  of FIG.  1 . The slider  110  could hold a mirror  70  of FIG. 7 for reflecting optical waves in switching applications, for example. Each set of vibromotor  10  contains three independent thermal actuators  20  electrically wired in parallel. The number of the thermal actuators in a set could be adjusted depending on the load of the application. Wiring in parallel ensures a lower operating voltage for the system. Optionally, as seen in FIG. 7, a second set of actuators at −45 degrees would be used to give the motor bi-directional capability. However, the ability to use one set of actuators to drive the motor in both directions would reduce its size, a critical constraint in some applications. 
     As a basic actuation element in this vibromotor, the thermal actuator  20  is utilized for its inherent low power level, fairly large force, and long-term reliability features. As a force generator, the thermal actuator  20  serves as an important energy converter, converting applied electrical energy to thermal energy and then to mechanical energy. The basic framework or body of the thermal actuator  20 , absent the impact head  40 , is a typical U-shaped, single-material, asymmetrical microstructure thermal actuator, as shown in FIG.  2  and known in the art. The temperature of the actuator body structure is raised due to the joule heating effect when applying an electrical current across the two anchors  210  and  220  at the ends of the structure. Because the cross-sectional areas of the thick arm  240  and thin arm  230  or beams are different, the higher electrical resistance in the thin arm  230  results in a higher temperature compared to that of the thick arm  240 . The effect of unequal thermal expansion of the structure is amplified by a joint between the thick arm  240  and the thin arm  230  at the tip, resulting in a lateral movement of the actuator tip towards the thick arm  240  side. A deflection as large as 15 μm can be achieved in the actuator  20 . The dimensions of the actuator  20  are optimized to deliver the highest force at any power. 
     Mechanical power transmission occurs during the impact of the thermal actuators  20  on both sides of a slider  110 . The slider  110 , used as a mechanical linkage, is composed of two parallel beams (15 μm wide each) connected at both ends. The intention behind narrow beams is to make the sides of the slider slightly more compliant when pushed on. This y-direction compliance assures that more friction is generated when the head  40  of the thermal actuator  20  is in contact with the slider  110 . In order to lessen the friction due to the surface-to-surface contact between the moving slider  110  structure and a substrate  111  underneath, dimples  250  are added under the slider  110  and the structures that are attached to it. To achieve higher forces, the initial gap (2 μm) between the slider  10  and the head  40  of the thermal actuator  20  are made as small as possible (limited by the resolution of the process). Small deflections will also greatly lower the power consumption of this vibromotor. Guide flanges  120  are used to constrain the slider  110  on the substrate  111  and to guide the slider  110  in a desired direction with minimum wobbling. The guide flanges  120  sit on the outside of the slider  10  to reduce the friction with the slider  110  during impact actuation of the head  40 . 
     Referring to FIG. 2, a top view representation of the thermal actuator  20  of FIG. 1 is shown. The following are examplary dimensions of the actuator  20 . The thin arm  230  is 200×2.5 μm while the thick arm  240  is 135×15 μm. The flexure  260  is 65×2 μm, and the gap between the thin and thick arms is 2 μm. The head  40  of the thermal actuator  20  includes a tip that is 2 μm in length and having a 20 μm-long 28 degree slightly curved slope of the triangular tip, as shown in FIG.  4 . The head  40  is designed in a suitable shape such that it has two modes of operation, which enables it to have bi-directional travel, depending on the level of current applied. 
     In contrast with prior-art micromotors, a typical energy-coupling element, such as the tooth-shaped drive yoke used in some stepper motors or a coupling gear in a microengine, is not needed in the driving mechanism design of the present invention. As a result, problems like gear backlash and improper impact contact that are often encountered due to the bearing clearances and improper tooth profile design can be minimized. 
     Hence, the ETV motor as taught by the present invention has minimum structural complexity, which increases its reliability and also has some other advantages. Since there is no additional coupling element needed between the slider  110  and a force generator (the thermal actuator  20 , in this case.) direct coupling is possible. This direct coupling is much more efficient since no energy is lost in those extra components. No complicated sequence signal is required to drive different components in the device. In the present invention, each thermal actuator  20  in an array works independently without any linkage in between. In some prior-art devices, a mechanical linkage has to be used between the thermal actuators to increase the output force. However, additional energy is lost in the bending of these linkages. 
     The electrothermal vibromotor (ETV motor) is fabricated using the Multi-User MEMS Process (MUMPS) available at the Microelectronics Center of North Carolina (MCNC). In this surface micromachining process, low-pressure chemical vapor deposition (LPCVD) polysilicon is used as the structural layers and LPCVD phosphosilicate glass (PSG) is used for the sacrificial layers. A blanket 0.6 μm low-stress LPCVD silicon nitride layer is first deposited on the silicon wafers for electrical isolation. The first 0.5 μm-thick polysilicon layer is used to define the electrical interconnections and the electrical ground planes for the device. All the sliders  10  and the thermal actuators  40  are defined in the second 2 μm-thick polysilicon layer. The third 1.5 μm-thick polysilicon is used to define the guide flanges  120  only. Two PSG layers with thickness&#39; of 2 μm and 0.75 μm, respectively, are deposited between the structural polysilicon layers. A final 0.5 μm-thick gold layer is deposited on the electrical probing pads. To release the structure from the oxide the sample is immersed in a bath of concentrated hydrofluoric acid (HF) at room temperature for 8 minutes. This is followed by several minutes of rinse in deionized water and then in isopropanol alcohol (IPA) bath for 15 minutes. Finally, the chip is dried in an oven at 110° C. for 15 minutes. No significant stiction was observed after release. Because of its structural simplicity the vibromotor  10 , as taught by the present invention, has high yields. 
     In accordance with the teachings of the present invention, the motion of the slider  110  depends on the impact between the thermal actuator head  40  and the slider wall. Using the sloped flat head as one embodiment of the present invention of the impact head  40 , the direction of travel for the slider  110  can be controlled by the amount of current, high or low level, through the thermal actuator  20 . 
     Referring to FIG. 3, the basic driving mechanism of the current-controlled bi-directional electrothermal vibromotor  10  of FIG. 1 is shown. In the initial rest position  300  of the head  40  of the thermal actuator  20 , there is some space or gap between the wall of the slider  10  and the head  40 , before impact. When driven with lower currents (Push Mode), the slider  110  moves forward (the direction to which the thermal actuator  20  swings or taps much like the motion of a chicken pecking). This forward motion can been visualized looking at how the dimple  250  moves ahead of the actuator head  40 , from representations  301  to  303 , after each impact when the space between the head  40  and the slider  110  is closed or otherwise removed. Such actuator impact motion, swing, or pivoting contact is much like the tapping of a woodpecker&#39;s bill on a stationary tree or a sliding woodpecker on a stationary pole toy. 
     In the Push Modes of  301  and  303 , the tip of the thermal actuator&#39;s head  40  makes contact with the slider  110  and keeps pushing. The preferably slope-shaped design of the head  40  causes the friction between the head  40  and the slider  10  to increase as the actuator  20  continues to deflect causing more contact and greater normal force exerted on the slider  110 . At some point  303 , the friction becomes large enough so that the head  40  grips the slider  110  and the slider  110  is pushed forward during the rest of the thermal actuator&#39;s forward swing. As the head  40  swings back it releases itself from the slider  110 . 
     At higher currents (Pull Modes  304  and  306 ), a larger deflection of the thermal actuator  20  pushes the head  40  harder into the slider  110 . Because the body of the thermal actuator  20  is framed by the two beams  230  and  240  of FIG. 2, the actuator  20  also acts as a spring pushing against the slider  110 , making sure the head  40  is in full contact with the slider  110 , as can be seen by representation  304 . When the head  40  of the thermal actuator  20  starts to swing back, there is still friction between the head  40  and the slider  110 , which pulls the slider in the backward direction as seen in representation  306 , again referencing the dimple  250  movement from representations  304  to  306 . Even though the speed is extremely high, the slider speed in the two directions are not equal because of the different impact conditions. 
     Referring to FIG. 8 for a more detailed explanation, there are two modes of operation for the actuator  20  of FIG. 1, as previously discussed. One is the lower current Push Mode, where the slider  110  can be pushed forward (the direction to which the thermal actuator  20  including its head  40  swings). The other is the higher current Pull Mode, where the slider  110  can be pulled backwards. The first representation  800  shows the initial rest position of the impact head  40  with respect to the wall of the slider  110 . The distance between a tip section of the impact head  40  and the wall of the slider  110  is denoted as a, while b is the distance between a tail section of the impact head and the wall of the slider  110 . Because the slope of the tail section is steeper, more inclined, or otherwise corresponding less to the shape of the slider  110 , distance b is also greater than distance a. The thermal actuator  20  of FIG. 2 will start to swing back and forth when supplied with an AC signal. During the thermal actuator&#39;s forward swing  801  to  803 , the impact head  40  moves inward to the slider  10  and closes the gap before the tip of the head  40  touches the wall. Because the thermal actuator  20  is somewhat compliant in the y-direction due to its two-beam structure, the tip of the impact head  40  will act as a pivot point and the head  40  rotates as the thermal actuator  20  continues pushing into the slider  110 , making b&lt;1 μm in  803 . The friction between the impact head  40  and the wall of the slider  110  will increase, proportionally to the normal force  84  exerted on the slider  110 , and at some point, grasps the slider  110  and push it forward as denoted in  803 . Before the whole impact head  40  makes full contact with the slider (b=0), the head  40  of the thermal actuator starts to swing back, releasing itself from the slider  110  in  805 . The impact head  40  will then go back to its initial position, preparing for the next swing in the Push Mode situation. 
     However, in the Pull Mode  806 ,  808 , and  810 , due to the higher current applied, the impact head  40  will rotate further and makes full contact (b=0) while the head  40  of the thermal actuator keeps pushing inward to the slider in  808 . Now the head  40  of the thermal actuator acts like a gripper that clamps the slider  110  in position, and the energy is stored in the bending of the thermal actuator  20  of FIG.  2 . When the head  40  of the thermal actuator starts to swing back, a partial force in the x-direction  86  is exerted on to the slider  110  while the impact head  40  rotates back, which pulls the slider  110  to move backwards in  810 . Then the head  40  releases from the slider  110  and back to its initial position, waiting for another cycle. As noted before, because of different impact conditions in these two modes, the speed of the slider  110  will not be the same as it moves in the two directions. 
     Conventional thermal actuators reported to date have used a driving signal of either a DC voltage or a voltage square wave with a 50% duty cycle. Usually a strong decrease in the deflection of beams that are 200 μm in length is observed when driven by signal frequencies up to 1.5 kHz. Although a higher deflection can be achieved at this frequency by increasing applied current, it often leads to permanent plastic deformation of the thin arm. This occurs when the brittle-to-ductile transition temperature is reached in the thin arm which cannot dissipate the excess heat fast enough. The stress on the two ends of the arm leads to buckling, causing the actuator to bend back and change its rest position from that of the initial state. This not only limits the driving frequency and speed of the electrothermal vibromotor, but also is a detriment to its lifetime. To improve its frequency performance, the effect of the driving signal has been explored. 
     When driven at frequencies above 4.5 kHz with a sinusoidal AC signal, a conventional thermal actuator responds with a fixed deflection rather than oscillation. This is because the cooling of the conventional thin arm can no longer keep up with the driving frequency. Although oscillation on top of this offset deflection can be seen by increasing the applied current, the swing amplitude is so small (&lt;1 μm) that it is generally not useful. Furthermore, it would often quickly lead to permanent plastic deformation of the thin arm, or even fuse the device. This not only limits the maximum possible driving frequency, and thus the speed of the ETV motor, but also is a detriment to its lifetime, as previously mentioned. 
     Theoretically, reducing the thermal time constant through optimized thermomechanical design can increase the frequency performance of the actuator, however, the use of an AC+DC driving signal has been found to improve the performance of the system. The swing amplitude can be increased enormously at high frequencies by adding a DC bias on top of the sinusoidal AC signal. Under this driving condition, the thermal actuator oscillates from a point that is different from the initial rest position. This new starting point is the offset deflection caused by the high frequency AC, as described earlier. This method opens up a possibility for thermal actuators to be safely tuned to a much higher frequency while still having useful swing amplitudes. The highest frequency observed in the actuator  20  is above 70 kHz. 
     The power dissipated in the thermal actuator is equal to I 2 R, where I is the amount of current applied and R is the resistance of the beams. This energy raises the temperature of the actuator, while the heat is dissipated mainly through conduction via the anchor to the substrate, and convection and radiation to the ambient air. If the square of the input current (I 2 ) versus time (t) is plotted, the area under the curve is proportional to the energy input to the system over a period of time. There exists a “threshold” area under the curve for a specific period of time, above which plastic deformation will occur. This threshold will depend on the heat dissipation rate under the applied current condition during that period of time. 
     For a sinusoidal AC voltage input, the I 2 −t plot will look like the one shown in FIG. 5 a , assuming that the resistance of the thermal actuator does not change with time. As the actuator is driven to higher frequencies, the amplitude of the deflection decreases. Increasing the current driving the actuator as is shown in FIG. 5 b  can compensate for the decrease in deflection. However, at a certain frequency, governed by the thermal time constant of the element, the actuator will no longer work. A reduction of the thermal time constant through optimized thermomechanical design can increase the frequency performance of the actuator and increase the speed of the vibromotor. However, because of the magnitude of the input current, the temperature of the element could easily pass the threshold for plastic deformation. 
     In accordance with the teachings of the present invention, a waveform consisting of a sinusoidal AC voltage offset by a DC bias as shown in FIG. 5 c  is applied. The DC bias will cause a deflection of the actuator  20  reducing the gap between the head  40  and the slider  110 . The time of impact occurs sooner due to the ac voltage improving the motor performance. This I 2 −t plot of the faster impact is shown in FIG. 5 d . Because current never reaches zero due to the DC offset, the total energy fed into the system is greatly increase. Hence, the peak voltage level needed to reach the desired deflection is reduced. The frequency of impacts is reduced by a factor of two compared to that of a pure ac signal where impact occurs at both the positive and negative peak. This operation method allows the thermal actuator  20  to be safely tuned to a much higher frequency. 
     The testing of the electrothermal vibromotor, in accordance with the present invention, was conducted in an open bay lab. The test setup consisted of a probe station, a function generator, a DC power supply, two multimeters and a CCD camera attached to the microscope. Video was recorded on a computer for analysis. 
     First, a 200 Hz sinusoidal AC voltage input (no DC bias) was used to drive the electrothermal vibromotor  10  of FIG.  1 . The amplitude of the voltage was increased from 0 V to a level where the head  40  of the thermal actuator  20  starts to tap or otherwise provide impact to the slider  110  but not enough to make full area contact with the slider  110 . At this point the slider will start to move forward, as in FIG. 8.1B. Observation of how the head  40  of the thermal actuator  20  contacts the slider  110  is straightforward because the image is a superposition of the vibrating element. When the applied voltage is further increased, the slider  110  will suddenly change its direction and starts to move backward, as in FIG. 8.2C. Travel across the full range (390 μm) of the actuator  20  of FIG. 2, in both directions was observed though the speed was inconsistent. This inconsistency was due to variation in the step sizes from factors such as the friction with the substrate  111  and the guide flanges  120  of FIG.  1 . The ability to drive the electrothermal vibromotor with AC signal frequencies above 2 kHz was achieved. Applied AC voltages to the system range from 5.4 V to 6.6 V, and the total current (for six thermal actuators  20 ) were measured from 18.3 mA to 23.0 mA. The change from forward actuation to backward actuation can be controlled by increasing the AC voltage by about 1 volt. Typically, prior-art thermal actuators are not expected to move at such high frequencies, however, in this case the structures and the deflections are small (microns) for the actuators  20  as taught by the present invention. 
     A 2 V sinusoidal AC signal at 5 kHz plus a 10 V DC bias, which corresponds to a total current of 49.6 mA can be used, as an example, to drive the thermal elements or actuators  20 . The measured total current for both operation modes is plotted in FIG.  6 . Under this driving signal, travel in both directions was very smooth. It was also very easy to change the direction of motion by simply adjusting the DC bias level (plus or minus 1 volt). The traveling speed observed is proportional to the driving frequency. From the recorded video, a speed above 3 mm/set was measured for the slider  110 . Backward motion of the slider was faster than the forward motion. This is expected because the head  40  is in full contact longer during the Pull Mode, as depicted in FIG. 8.2B. Driving the thermal elements or actuators  20  at 10 kHz has been done by tuning the AC signal to 4 volts. The force generated by this AC+DC operation appears much larger than when driving with pure AC. Furthermore, the ability to drive the slider  110  with only one set of thermal actuators  20  on only one side of the slider  110  was achieved. In some situations, even one thermal actuator  20  alone is enough to move the slider  110 . 
     A round-headed thermal actuator  440 , as shown in the picture insert in FIG. 4, has been included as a test structure and shows only the Pull Mode operation or backward travel motion. This alternate design could be used in applications where only one traveling direction is needed or similar traveling speed in two directions is preferred. 
     Referring to FIG. 7, a scanning electron microscope (SEM) photograph of a fiber optic switch with an integrated electrothermal vibromotor  10  of FIG. 1, in accordance with the present invention is shown. As a demonstration of this electrothermal vibromotor  10  of the present invention, it was coupled with a gear 300 μm in diameter, making a rotation stage for optical applications a possibility. In addition, the motor was used to drive a vertical micromirror  70  that was designed for a free space optical fiber switch. The micromirror has a dimension of 300×400 μm and could be move back and forth over the full travel range of 350 μm. 
     Hence, a compact polysilicon surface-micromachined electrothermally actuated vibromotor  10  of FIG. 1 is taught by the teachings of the present invention. Mechanical power transmission occurs during the impact of the thermal actuators  20  on the sides of a movable guided slider  10 . Current-controlled bi-directional operation is made possible through the impact head design  40  having at least two different edges. A traveling speed of at least 3 mm/sec was measured when driven with a 2.0 V AC input signal at 5 kHz plus a 10.0 V DC bias offset. The electrothermal vibromotor  10  has been actuated with thermal elements or actuators  20  driven at frequencies above  19  kHz. As a demonstration, a hinged vertical micromirror  70  designed for free-space fiber-optic switch systems has been moved back and forth over a full range of 350 μm. 
     It will be apparent to those skilled in the art that various modifications and variations can be made to the present invention without departing from the spirit and scope of the invention. Thus, it is intended that the present invention cover the modifications and variations of this invention provided they come within the scope of the appended claims and their equivalents.

Technology Category: 7