# Patent

## Title
Ultrasound transducers with improved focus in the elevation direction

## Abstract

A phased array ultrasound transducer is made from a plurality of independently excitable elements that are arranged in a row in the azimuthal direction, configured so that azimuthal aiming of an outgoing ultrasound beam is controlled by timing the excitation of the elements. The geometry of the elements is configured to focus the outgoing beam in the elevation direction so as to improve the images of target regions located at or about a particular radial distance. In some embodiments, this is accomplished by forming each element from a plurality of subelements that are stacked in the elevation direction, with the subelements of any given element all (a) wired together and (b) positioned at about the same distance from a substantially rod-shaped focal region.

## Background
CROSS REFERENCE TO RELATED APPLICATIONS
This application is a continuation-in-part of U.S. application Ser. No. 10/996,816, filed Nov. 24, 2004, which claims priority to U.S. provisional application No. 60/525,330, filed Nov. 26, 2003.


BACKGROUND
In the medical field, monitoring heart function impacts critical decisions that relate to patient care. One type of prior art heart monitor is the intravascular/intracardiac ultrasound transducer (such as the AccunavTM transducer). This type of transducer, however, is not well suited for transesophageal echocardiography because the transducer elements are oriented longitudinally instead of transversely, which limits the types of images that can be obtained. A second type of prior art heart monitor is the transesophageal echocardiography (TEE) transducer, which is transversely oriented. However, in order to produce repeatedly usable images, the azimuthal aperture of these transducers must be quite large (e.g., 10-15 mm in diameter for adults), which requires a correspondingly large probe. Because of this large probe, conventional TEE often requires anesthesia, can significantly threaten the airway, and is not well suited for long-term monitoring of the heart.
SUMMARY OF THE INVENTION
Transesophageal ultrasound imaging is implemented using a miniature transversely oriented transducer that is preferably small enough to fit in a 7.5 mm diameter probe, and most preferably small enough to fit in a 5 mm diameter probe. Signal processing techniques provide improved depth of penetration, despite the fact that the transducer is so small.



BRIEF DESCRIPTION OF THE DRAWINGS
FIG. 1 is an overall block diagram of a system for monitoring cardiac function by direct visualization of the heart.
FIG. 2 is a more detailed view of the probe shown in the FIG. 1 embodiment.
FIG. 3 is a schematic representation of a displayed image of the trans-gastric short axis view (TGSAV) of the left ventricle.
FIG. 4 depicts the positioning of the transducer, with respect to the heart, to obtain the TGSAV.
FIG. 5 shows a plane that slices through the trans-gastric short axis of the heart.
FIG. 6A shows an optional probe interface configuration.
FIG. 6B is a graph of gain characteristics for a TGC amplifier.
FIGS. 7A, 7B, and 7C show a first preferred transducer configuration.
FIGS. 8A and 8B show a second preferred transducer configuration.
FIG. 9 shows the components of spatial resolution.
FIG. 10 shows the interaction between the shape of the resolution voxel and the boundary.
FIG. 11 shows the sector width.
FIG. 12 is a schematic illustration of the paths of the ultrasound beam as it is swept through the sector.
FIG. 13 is a schematic illustration of the samples that correspond to a section of one of the beams of FIG. 12.
FIG. 14 is a flowchart of a processing algorithm that uses frequency characteristics of the return signal.
FIG. 15 is a graph of a function that maps a gain factor onto an energy ratio.
FIGS. 16A and 16B show two alternative transducer designs.
FIG. 17 is an isometric view of an alternative transducer design in which each element includes three stacked subelements.
FIG. 18A is an isometric view of an alternative transducer design with a curved front face.
FIG. 18B is a side view of an element of the FIG. 18A transducer.
FIG. 19 is a side view of an element of another alternative transducer in which each element includes three stacked subelements.
FIG. 20A is a side view of an element of yet another alternative transducer in which each element includes three stacked subelements.
FIG. 20B is a is an isometric view of the FIG. 20A transducer.



DESCRIPTION OF THE PREFERRED EMBODIMENTS
FIG. 1 is an overall block diagram of a system that may be used for continuous long term monitoring of cardiac function by direct visualization of the heart. An ultrasound system 200 is used to monitor the heart 110 of the patient 100 by sending driving signals into a probe 50 and processing the return signals received from the probe into images, using the image processing algorithms described below. The images generated by those algorithms are then displayed on a monitor 210, in any conventional manner.
FIG. 2 shows more details of the probe 50, which is connected to the ultrasound system 200. At the distal end of the probe 50 there is a housing 60, and the ultrasound transducer 10 is located in the distal end 64 of the housing 60. The next portion is the flexible shaft 62, which is positioned between the distal end 64 and the handle 56. This shaft 62 should be flexible enough so that the distal end 64 can be positioned past the relevant anatomical structures to the desired location, and the handle 56 facilitates the positioning of the distal end 64 by the operator. Optionally, the handle 56 may contain a triggering mechanism 58 which the operator uses to bend the end of the housing 60 to a desired anatomical position as described below.
At the other end of the handle 56 is a cable 54, which terminates, at the proximal end of the probe 50, at connector 52. This connector 52 is used to connect the probe 50 to the ultrasound system 200 so that the ultrasound system 200 can operate the probe. Signals for the ultrasound system 200 that drive the transducer 10 travel through the probe 50 via appropriate wiring and any intermediate circuitry (not shown) to drive the transducer 10, and return signals from the transducer 10 similarly travel back through the probe 50 to the ultrasound system 200 where they are ultimately processed into images. The images are then displayed on the monitor 210 in a manner well known to persons skilled in the relevant art.
In the preferred embodiments, the housing 60 has an outer diameter of less than 7.5 mm. The probe contains the ultrasound transducer 10 and connecting wires, and the housing 60 can be passed through the mouth or nose into the esophagus and stomach.
The returned ultrasound signals are processed in the ultrasound system 200 to generate an image of the heart. Preferably, additional signal processing is used to significantly improve image production, as described below. FIG. 3 shows a displayed image of the trans-gastric short axis view (TGSAV) of the left ventricle (LV), which is a preferred view that can be imaged using the preferred embodiments. The illustrated image of the TGSAV appears in a sector format, and it includes the myocardium 120 of the LV which surrounds a region of blood 130 within the LV. The image may be viewed in real time or recorded for later review, analysis, and comparison. Optionally, quantitative analyses of cardiac function may be implemented, including but not limited to chamber and vessel dimensions and volumes, chamber function, blood flow, filling, valvular structure and function, and pericardial pathology.
Unlike conventional TEE systems, the relatively narrow housing used in the preferred embodiments makes it possible to leave the probe in position in the patient for prolonged periods of time.
As best seen in FIGS. 4 and 5, the probe 50 is used to introduce and position the transducer 10 into a desired location within the patient's body. The orientation of the heart within the chest cavity is such that the apex of the left ventricle is positioned downward and to the left. This orientation results in the inferior (bottom) wall of the left ventricle being positioned just above the left hemidiaphragm, which is just above the fundus of the stomach. During operation, the transducer 10 emits a fan-shaped beam 90. Thus, positioning the transducer 10 in the fundus of the stomach with the fan-shaped beam 90 aimed through the left ventricle up at the heart can provide a trans-gastric short axis view image of the heart 110. The plane of the fan-shaped beam 90 defines the image plane 95 shown in FIG. 5. That view is particularly useful for monitoring the operation of the heart because it enables medical personnel to directly visualize the left ventricle, the main pumping chamber of the heart. Note that in FIGS. 4 and 5, AO represents the Aorta, IVC represents the Inferior Vena Cava, SVC represents the Superior Vena Cava, Pa. represents the pulmonary artery, and LV represents the left ventricle.
Other transducer positions may also be used to obtain different views of the heart, typically ranging from the mid-esophagus down to the stomach, allowing the operator to directly visualize most of the relevant cardiac anatomy. For example, the transducer 10 may be positioned in the lower esophagus, so as to obtain the conventional four chamber view. Transducer positioning in the esophagus would typically be done without fully flexing the probe tip, prior to advancing further into the stomach. Within the esophagus, desired views of the heart may be obtained by having the operator use a combination of some or all of the following motions with respect to the probe: advance, withdraw, rotate and slight flex.
For use in adults, the outer diameter of the housing 60 is preferably less than about 7.5 mm, more preferably less than about 6 mm, and is most preferably about 5 mm. This is significantly smaller than conventional TEE probes. This size reduction may reduce or eliminate the need for anesthesia, and may help expand the use of TEE for cardiac monitoring beyond its previous specialized, short-term settings. When a 5 mm housing is used, the housing is narrow enough to pass through the nose of the patient, which advantageously eliminates the danger that the patient will accidentally bite through the probe. Alternatively, it may be passed through the mouth like conventional TEE probes. Note that the 5 mm diameter of the housing is similar, for example, to typical NG (naso-gastric) tubes that are currently successfully used long-term without anesthesia in the same anatomical location. It should therefore be possible to leave the probe in place for an hour, two hours, or even six hours or more.
The housing wall is preferably made of the same materials that are used for conventional TEE probe walls, and can therefore withstand gastric secretions. The wiring in the probe that connects the transducer to the rest of the system may be similar to that of conventional TEE probes (adjusted, of course, for the number of elements). The housing is preferably steerable so that it can be inserted in a relatively straight position, and subsequently bent into the proper position after it enters the stomach. The probe tip may be deflected by various mechanisms including but not limited to steering or pull wires. In alternative embodiments, the probe may use an intrinsic deflecting mechanism such as a preformed element including but not limited to pre-shaped materials. Optionally, the probe (including the transducer housed therein) may be disposable.
For imaging the TGSAV of the LV, the probe tip is preferably ultimately “ante-flexed” (flexed towards the front of the patient) approx. 70-110 degrees. This may be implemented, for example, by building a triggerable ante-flex (e.g., on the order of 70 degrees) into the probe through a combination of a pre-formed element, a device to prevent flexing during insertion and a trigger to release the preformed element from the insertion limit once the probe is in the desired anatomic location. Optionally, a pull-wire may be used for steering to provide the additional 0-40 degrees of flex after the transducer is lowered to the appropriate depth. The triggerable ante-flex component is preferably designed so that it will present little resistance to returning to the unflexed position during probe removal.
FIG. 6A shows an optional configuration that is similar to the FIG. 1 embodiment, except that the circuitry that interfaces with the probe 50 is relocated to an interface box 203. The rest of the ultrasound system remains in the main processing unit 201, which communicates with the interface box 203 via an appropriate cable 205. The interface box 203 contains circuitry to amplify the signals from the transducer 10 and/or digitize those signals. Using such an interface box advantageously provides shorter signal paths for those parts of the circuit that are most sensitive to electrical noise (i.e., where the signals are small). The transmit signals that drive the transducer 10 may also be generated within the interface box 203 if desired.
Electrical noise may be further reduced using a variety of techniques. For example, in one embodiment, the interface box 203 houses a preamplifier that serves as the first stage in the amplification/processing chain, and separate power supplies are used for the interface box and the main processing unit 201 to reduce electronic noise pass-through. In another embodiment, the interface box 203 houses a preamplifier that serves as the first stage in the amplification/processing chain, and the preamplifier operates on battery power. For both of these embodiments, time gain compensation (TGC) is preferably implemented in that preamplifier. TGC compensates for the fact that the return signals from distant scatterers are weaker than those for nearby scatterers by increasing the gain for signals with longer travel time. TGC may be implemented using conventional techniques that are well known to persons skilled in the relevant art. An example of suitable gain vs. delay characteristics for TGC is shown in FIG. 6B, where the x-axis represents the delay between transmission of the ultrasound pulse and detection of the return signal, and corresponds to depth as follows:

Depth (in cm)=0.077 cm/μs×delay (in μs).

Implementing TGC in the preamplifier facilitates efficient digitization. The preamplifier may also provide amplitude compandoring (a form of compression) to further facilitate efficient digitization. Optionally, the preamplifier's output may be digitized in the interface box, in which case only digital signals would be sent from the interface box to the main processing unit to further reduce electrical noise. These digital signals may even be opto-isolated to eliminate all possible electrical connections in the return path, to reduce electrical noise pass-through further still.
The preferred embodiments described herein provide a good quality image of the TGSAV of the LV from a transducer that is small enough to fit in the narrow housing described above. FIGS. 7A-7C depict a first preferred transducer 10. FIG. 7A shows the location of the transducer 10 in the distal end of the housing 60, and also includes a top view 22 of the transducer 10 surrounded by the wall of the housing 60 and a front cutaway view 24 of the transducer 10.
As best seen in FIG. 7B, the azimuth axis (Y axis) is horizontal, the elevation axis (Z axis) is vertical, and the X axis projects out of the page towards the reader. When steered straight forward by energizing the appropriate elements in the transducer, the beam will go straight out along the X axis. The steering signals can also send the beam out at angles with respect to the X axis, in a manner well know to persons skilled in the relevant arts.
The transducer 10 is preferably a phased array transducer made of a stack of N piezo elements L1 . . . LN, an acoustic backing 12, and a matching layer in the front (not shown), in a manner well known to those skilled in the relevant art. As understood by persons skilled in the relevant arts, the elements of phased array transducers can preferably be driven individually and independently, without generating excessive vibration in nearby elements due to acoustic or electrical coupling. In addition, the performance of each element is preferably as uniform as possible to help form a more homogeneous beam. Optionally, apodization may be incorporated into the transducer (i.e., tapering the power driving transducer elements from a maximum at the middle to a minimum near the ends in the azimuthal direction, and similarly tapering the receive gain).
The preferred transducers use the same basic operating principles as conventional TEE transducers to transmit a beam of acoustic energy into the patient and to receive the return signal. However, while the first preferred transducer 10 shown in FIGS. 7A-7C shares many characteristics with conventional TEE transducers, the first preferred transducer 10 differs from conventional transducers in the following ways:









TABLE 1






conventional TEE
first preferred


Feature
transducer
transducer







Size in the transverse (azimuthal)
10-15 mm
about 4-5 mm


direction




Number of elements
64
about 32-40


Size in the elevation direction
2 mm
about 4-5 mm


Front face aspect ratio
about 1:5
about 1:1


(elevation:transverse)




Operating frequency
5 MHz
about 6-7.2 MHz









In FIG. 7A, the elevation is labeled E and the transverse aperture is labeled A on the front cutaway view 24 of the transducer 10. The location of the wall of the housing 60 with respect to the transducer 10 can be seen in the top view 22.

FIG. 7C shows more details of the first preferred transducer 10. Note that although only eight elements are shown in all the figures, the preferred transducer actually has between about 32-40 elements, spaced at a pitch P on the order of 130 μm. Two particularly preferred pitches are approximately 125 μm (which is convenient for manufacturing purposes) and approximately 128 μm (0.6 wavelength at 7.2 MHz). When 32-40 elements are spaced at a 125 μm pitch, the resulting azimuth aperture A (sometimes simply called the aperture) of the transducer 10 will be between 4 and 5 mm. The reduced element count advantageously reduces the wire count (compared to conventional TEE transducers), which makes it easier to fit all the required wires into the narrower housing. The kerf K (i.e., the spacing between the elements) is preferably as small as practical (e.g., about 25-30 μm or less). Alternative preferred transducers may have between about 24-48 elements, spaced at a pitch between about 100-150 μm.
A second preferred transducer 10′ is shown in FIGS. 8A-8B. This transducer 10′ is similar to the first preferred transducer 10 described above in connection with FIGS. 7A-7C, except it is taller in the elevation direction. Similar reference numbers are used in both sets of figures to refer to corresponding features for both transducers. Numerically, the second transducer differs from conventional transducers in the following ways:









TABLE 2






conventional TEE
second preferred


Feature
transducer
transducer







Size in the transverse (azimuthal)
10-15 mm
about 4-5 mm


direction




Number of elements
64
about 32-40


Size in the elevation direction
2 mm
about 8-10 mm


Front face aspect ratio
about 1:5
about 2:1


(elevation:transverse)




Operating frequency
5 MHz
about 6-7.2 MHz









In alternative embodiments, the transducer 10 may be built with a size in the elevation direction that lies between the first and second preferred transducers. For example, it may have a size in the elevation direction of about 7.5 mm, and a corresponding elevation:transverse aspect ratio of about 1.5:1.
The transducer 10 preferably has the same transverse orientation (with respect to the axis of the housing 60) as conventional TEE transducers. When the transducer is positioned in the stomach (as shown in FIG. 4), the image plane (azimuthal/radial plane) generated by the transducer intersects the heart in the conventional short axis cross-section), providing the trans-gastric short axis view of the heart, as shown in FIGS. 3 and 5. The transducer is preferably as wide as possible in the transverse direction within the confines of the housing. Referring now to the top view 22 in FIG. 7A, two examples of transducers that will fit within a 5 mm housing are provided in the following table, along with a third example that fits in a housing that is slightly larger than 5 mm:










TABLE 3






first
second
third


Parameter
example
example
example







number of elements in the transducer
38
36
40


a (azimuthal aperture)
4.75 mm
4.50 mm
5.00 mm


b (thickness)
1.25 mm
2.00 mm
2.00 mm


c (inner diameter of housing at the
4.91 mm
4.92 mm
5.39 mm


transducer)





housing wall thickness
0.04 mm
0.04 mm
0.04 mm


outer diameter of housing
4.99 mm
5.00 mm
5.47 mm









Referring now to the top view 22 in FIG. 8A, the three examples in Table 3 are also applicable for fitting the second preferred transducer 10′ within a 5-5.5 mm housing.

The above-describe embodiments assume that the housing is round. However, other shaped housings may also be used to house the transducer, including but not limited to ellipses, ovals, etc. In such cases, references to the diameter of the housing, as used herein, would refer to the diameter of the smallest circle that can circumscribe the housing. To account for such variations in shape, the housing may be specified by its outer perimeter. For example, a 5 mm round housing would have a perimeter of 5 p mm (i.e., about 16 mm). When a rectangular transducer is involved, using an oval or elliptical housing can reduce the outer perimeter of the housing as compared to a round housing. For example, an oval that is bounded by a 6 mm×2 mm rectangle with its corners rounded to a radius of 0.5 mm contains a 5 mm×2 mm rectangular region, which can hold the third example transducer in Table 3. Allowing for a 0.04 mm housing wall thickness yields an outer perimeter of 15.4 mm, which is the same outer perimeter as a 4.9 mm diameter circle. The following table gives the outer perimeters that correspond to some of the diameters discussed herein:









TABLE 4






outer diameter
outer perimeter




















2.5
mm
8
mm



4

13




5

16




6

19




7.5

24









Since the characteristics of the last one or two elements at each end of the transducer may differ from the characteristics of the remaining elements (due to differences in their surroundings), the last two elements on each side may be “dummy” elements. In such a case, the number of active elements that are driven and used to receive would be the total number of element (shown in Table 3) minus four. Optionally, the wires to these dummy elements may be omitted, since no signals need to travel to or from the dummy elements. Alternatively, the wires to may be included and the last two elements may be driven, with the receive gain for those elements severely apodized to compensate in part for their position at the ends of the transducer.
Preferably, conventional beam-forming techniques are used to generate and aim a beam of acoustic energy in the desired directions. For example, focusing in the azimuthal direction may be accomplished by phasing (i.e., timing the excitation of individual elements L1 . . . LN in the array, and using appropriate time delays in the returns of individual elements before summing the respective returns into an ultrasound return signal). Focusing in the elevation direction may be accomplished based on the near-field and far-field properties of the sound signal, and will depend upon the physical height of the elements in the elevation direction and optional acoustic lenses.
Resolution adequate to determine LV size and function depends upon a combination of resolution in azimuth, elevation, and axis. This combination is referred to as “spatial resolution” and is illustrated in FIG. 9. FIG. 9 shows the image plane 320 and a scan line 310 that lies on the image plane 320. The axial direction AX is defined by the scan lines 310, and the transducer (not shown) is located far back along the AX axis. Out at the voxels being imaged, the azimuthal direction AZ is perpendicular to the AX axis within the image plane 320, and the elevation axis EL is perpendicular to the image plane 320. In an ideal system, each voxel would be a point. In real-world systems, however, the voxels have a volume that is defined by the resolution in all three directions AX, AZ and EL, as shown for voxel 330. Similarly, while the image plane 320 is depicted as a thin plane, the real-world image plane will have a thickness in the elevation direction EL that is equal to the thickness of the voxel 330 in the elevation direction.
The general formula for azimuthal and elevation resolutions is:

Δθ≈1.22 λ/d,

where Δθ denotes the beam width in radians, λ the wavelength (corresponding to the transducer center frequency) and d the aperture in the given direction (azimuth or elevation). The wavelength λ and aperture d are measured in the same units (e.g., μm).

Axial resolution depends indirectly upon the wavelength λ. Although the inventors are not aware of any specific formula for axial resolution, it is typically on the order of 16-64 times the wavelength. Thus, increasing the center frequency increases all three components of spatial resolution. A center frequency on the order of5-10 MHz is high enough to provide adequate resolution.
FIG. 10 illustrates the interplay between the three components in determining the interaction between the shape of the resolution voxel and the boundary orientation in detecting and determining boundaries. It shows the same voxel 330 that appears in FIG. 9, and also shows an illustrative piece 340 of the boundary being imaged that coincides with that voxel. If the boundary orientation is random with respect to the resolution voxel, one suitable approach is to make the resolution voxel as cubical as possible. In order to obtain that shape, the azimuth and elevation resolutions for a given voxel should be approximately equal, which occurs when the front face of the transducer is approximately square, as it is for the first preferred transducer discussed above in connection with FIGS. 7A-7C.
For the first preferred transducer, the elevation aperture is approximately the same as the azimuth aperture. In other words, the front face of the transducer has a elevation:transverse aspect ratio that is approximately 1:1 (i.e., it is approximately square). A square transducer with a width of 4-5 mm in the transverse direction would therefore have an area of approximately 16-25 mm2 .
The formulas for azimuthal and elevation resolution are:

ΔθAZ=1.22×λ/dAZ 

and

ΔθEL=1.22×λ/dEL 

where ΔθAZ and ΔθEL are the azimuth and elevation resolutions, respectively, (both measured in radians); and dAZ and dEL are the azimuth and elevation apertures, respectively. These components may be combined into a single equation for overall resolution as a function of area and frequency, as follows:

ΔθOVERALL=1.5×λ2/(dAZ×dEL)

As explained above, increasing the center frequency results in increased resolution. However, increasing the center frequency also reduces the penetration depth due to frequency-dependent attenuation, which is governed by the approximate formula

a≈0.5f×r

where a denotes the one-way attenuation in dB, f is the center frequency in MHz, and r the depth in cm. Thus, one-way frequency dependent attenuation will typically be about 0.5 dB MHz−1 cm−1 and typical round-trip frequency dependent attenuation will typically be about 1 dB MHz−1 cm−1.

The inventors have determined that a transducer center frequency between about 6 and 7.2 MHz provides a good trade-off between resolution and depth of penetration for TEE using a transducer with a 4.75 mm azimuthal aperture. In the embodiments described herein, that range of frequencies can typically provide enough depth of penetration to image the far wall of the left ventricle (in the TGSAV) so that the interior volume of the left ventricle can be computed. (In most subjects, a 12 cm depth of penetration is adequate to image the far wall. For many subjects, a depth of penetration of about 9-10 cm will suffice).
When the transducer elements are spaced at a 125 μm pitch, using a transducer center frequency of 6.16 MHz is particularly advantageous because it corresponds to a wavelength of λ=250 μm. At that wavelength, the elements are spaced at a pitch of 0.5λ, which is sometimes referred to as “half-wavelength pitch”. As is well known to those skilled in the art, a half-wavelength pitch is excellent for eliminating grating lobes while still minimizing element count for a given azimuth aperture. Somewhat larger pitches, e.g. 0.6λ, still work reasonably well in terms of eliminating grating lobes. Thus, for transducers that can operate at a range of center frequencies, acceptable performance can be maintained even if the frequency is increased about 20% (i.e., to the point where the pitch becomes about 0.6λ).
As explained above, the formula for the angular resolution is θ≈λ/d. Referring to the tables above, the first example of the first preferred transducer has a 38 element transducer with a 125 μm pitch, resulting in a 4.75 mm transducer width (d=4750 μm). It is preferably approximately square and operates at a center frequency of 6.16 MHz (λ=250 μm). When those values for d and λ are plugged into the equation for resolution, the result is θ≈0.053 radians, which converts to approximately 3 degrees resolution in both azimuth and elevation.
The increased size of the transducer in the elevation direction helps improve the angular resolution of the system in the elevation direction (as compared to a conventional TEE transducer with a 2 mm elevation). This increased resolution in the elevation direction helps compensate for losses in angular resolution in the azimuth direction caused by shrinking the azimuthal aperture down to about 4-5 mm.
The inventors have noticed that increasing the size of the transducer in the elevation direction further, so that it is larger than the size in the azimuthal direction provides improved performance when imaging the far wall of the heart in the TGSAV. This increase in transducer elevation causes the resolution voxel to shrink in the elevation direction at distances that correspond to the far wall of the LV, which results in increased resolution in the elevation direction. The inventors believe that increasing resolution in this direction is helpful at least in part because the far wall is slanted about the Y axis with respect to the front face of the transducers. (The Y axis is shown in FIG. 8B.) Shrinking the size of the voxel in the elevation direction therefore minimizes the variations of the components of return signals arising from specular reflections that fall within a single voxel.
The inventors have determined that the images of the TGSAV are better when the transducer is more than 1.5 times as large in the elevation direction as the transverse direction, and that the best images of the TGSAV are obtained when the transducer is about two times as large in the elevation direction as the transverse direction, as it is for the second preferred transducer 10′ described above in connection with FIGS. 8A and 8B and Table 2.
Instead of the 90° sector width that is typically used in conventional TEE systems, the preferred embodiment uses a smaller sector width (e.g., 60 degrees). Referring now to FIG. 11, a 60° sector 92 is shown emanating from the front face 14 of the transducer 10. The effective azimuthal aperture at an angle θ from the centerline CL can be obtained by multiplying the (nominal) azimuthal aperture (at θ=0) by cos(θ). Since cos(30°)=0.866 and cos(45°)=0.707, restricting the sector width to 60° (i.e., 30° on each side of the center line CL) causes a smaller degradation in worst-case azimuthal aperture: azimuthal aperture is degraded by only 13.4%, compared with 26.8% in the case of a 90° sector width. For example, the worst case aperture for a 4.75 mm wide transducer (5 mm housing diameter) in a 60° sector would be about 4.11 mm. The result is improved effective azimuthal aperture, which improves the overall resolution obtainable with small transducers. If a conventional 90° sector were to be used, a 5.82 mm wide transducer (6.1 mm housing diameter) would be needed in order to provide the same worst case aperture.
After a beam of ultrasound energy is sent into the patient using the transducer described above, the ultrasound return signal is received, preferably by the same transducer. The transducer converts the ultrasound return signal into an electrical return signal. This process continues as the beam is swept through the imaging sector. FIG. 12 is a schematic illustration of the path of the ultrasound beam as it is swept through the sector, first along line B1, then along line B2, and continuing on through line BM. These scan lines B1 . . . BM correspond to the fan-shaped beam 90 (shown in FIG. 4) and the sector 92 (shown in FIG. 11). Although the illustration only includes a small number (M) of scan lines, an actual system would have many more scan lines that are much more densely packed, so as not to adversely impact the azimuthal resolution.
The electrical return signal can be modeled as being an amplitude-modulated signal, with the carrier frequency at the center frequency, and with the modulation being caused in large part from scatterer spacing and other tissue characteristics such as the presence of connective tissue around heart muscle bundles. The electrical return signal is demodulated and digitized (i.e., sampled) to form a demodulated and digitized return signal (DDRS). A variety of conventional techniques that are well known to persons skilled in the relevant arts may be used to form the DDRS. One example is to digitize the electrical return signal and then rectify the result (i.e., take the absolute value) to form a rectified digitized ultrasound return signal. Another example is to rectify the electrical return signal in analog form, and then digitize the result to form the DDRS. Alternative demodulation approaches may also be used to extract the modulation information from the electrical return signal, including but not limited to coherent demodulation, Hilbert transforms, and other demodulation techniques that are well known to persons skilled in the relevant arts.
FIG. 13 is a schematic illustration of the DDRS that corresponds to a section of one of the ultrasound beams B1 . . . BM of FIG. 12. Each sample is represented by a dot S0 . . . S143. Each sample corresponds to a point in 2D space based on the direction of the beam and the time it took for the signal to travel from the transducer to the point in question and back. For example, if the return signal is digitized at 50 MHz, the time between samples will be 0.02 μs, which corresponds to a distance of 0.015 mm (based on the speed of sound in the body). Although the illustration only includes only 144 samples, an actual system would have many more samples in each scan line to provide the desired resolution. For example, to obtain a depth of penetration of 12 cm with the samples spaced 0.015 mm apart, 8000 samples would be needed. Because the beam of ultrasound energy is swept about a center point, polar coordinates are useful to organize the samples, at least in this stage of the processing. In some embodiments, the samples are analyzed entirely in polar coordinates, and only converted into rectangular coordinates for viewing on a conventional computer monitor. In other embodiments, the sample space may be converted into rectangular coordinates at an earlier stage of processing. The remaining explanation considers coordinates along each scan line (constant θ in the (r, θ) polar coordinate system, with r varying along the scan line), and pixel data associated with the center of the pixel along the scan line. Conversion to a sector image is well known in the field of ultrasound imaging.
The samples of each scan line are preferably processed by two different algorithms: one algorithm that analyzes intensity characteristics of the samples, and one algorithm that analyzes frequency characteristics of the samples.
For the first algorithm (i.e., the intensity algorithm) the samples of the scan line is divided into a plurality of pixels, with each pixel containing a plurality of samples. In the FIG. 13 example, each pixel contains 16 samples, as indicated by the boxes labeled “WIAP j” (which stands for “Window for Intensity Algorithm for Pixel j, where j is an integer from 0-8) that appear below the corresponding samples. Pixel data generated by signal processing is associated with the center position of the corresponding pixel. Of course, other numbers of samples per pixels could also be used instead of 16. In one preferred embodiment, for example, each pixel contains eight samples. The intensity algorithm is preferably a conventional image processing algorithm that converts the samples into a conventional image. The intensity for any given pixel is determined based on the amplitude of the samples that correspond to that pixel, with higher intensities corresponding to larger amplitudes. In the case of a 16 sample pixel, the average of those 16 samples would be used to determine the intensity at the pixel (with higher average intensity values appearing brighter and lower average intensity values appearing darker). Optionally, the intensity level of the pixel (or the samples that make up that pixel) may be compressed using conventional procedures such as logarithmic compression.
The second algorithm (i.e., the frequency algorithm) analyzes the frequency characteristics of the sample space and determines the spatial frequencies in scatterer spacing. Examples of suitable algorithms are described in U.S. Pat. No. 5,417,215 (hereinafter “the '215 patent”), which is incorporated herein by reference. The article “Spectral Analysis of Demodulated Ultrasound Returns: Detection of Scatterer Periodicity and Application to Tissue Classification” by S. Roth, H. M. Hastings, et al., published in Ultrasonic Imaging 19 (1997) at pp. 266-277, is also incorporated herein by reference.
The frequency algorithm provides a second result for each pixel in the image (i.e., in addition to the result produced by the intensity algorithm). Because most frequency analyzing algorithms provides better results when a larger number of data samples is used, and because each pixel only has a limited number of samples, samples on either side of the pixel in question are preferably combined with the samples in the pixel itself to increase the number of samples. In the illustrated example, each pixel contains 16 samples, but the frequency algorithm for any given pixel operates on 64 samples that are preferably centered in the pixel, as indicated by the boxes labeled “Window for Freq. Algorithm for Pixel k” (where k is an integer from 2-6) that appear below the samples. In this case, for example, all the samples from pixels 2-4 plus half the samples from pixels 1 and 5 would be used to perform the frequency analysis for pixel 3. Of course, other numbers of samples could be used for the frequency analysis instead of 64. Powers of 2, however, are preferable when a fast Fourier transform (FFT) algorithm is used. Optionally, windowing techniques (such as Hamming windows) may be used to weight the samples in the center more heavily than the samples that are near the ends.
FIG. 14 is a flowchart of a suitable frequency algorithm. In this algorithm, steps 1 and 2, taken together, attempt to discern the material that the pixel in question is made of (and more specifically, whether that pixel is blood or muscle) based on the frequency characteristics of samples in the pixel and the samples in the neighboring pixels.
In step 1, a Fourier analysis is performed on the samples to determine the power distribution in the various frequency bands at each pixel. The end result of the Fourier analysis of step 1 is a set of amplitude coefficients for each of a plurality of different frequencies, for each of the pixels (i.e., one set of coefficients for the first pixel, a second set of coefficients for the second pixel, etc.). The Fourier analysis may be implemented using any of a variety of algorithms that are well known to persons skilled in the relevant arts (e.g., a conventional FFT algorithm). Alternative embodiments may use other frequency analysis tools to achieve similar results, such as bandpass techniques (preferably integer-based FIR recursive), wavelet techniques, etc. In step 2, the ratio of power in a selected frequency band to the power in the entire spectrum for each pixel is computed. Thus, for each pixel, the following formula applies:

R=EBAND/ETOTAL 

Where EBAND is the power in the selected frequency band, ETOTAL is the total power in the portion of the spectrum, and R is the ratio of those two powers. When a Fourier analysis is used, the power in any given band equals the sum of the squares of the amplitudes of the Fourier coefficients within the band. The “selected frequency band” in this step is preferably selected so that changes in the ratio R are correlated to differences in the material that is being imaged (e.g., blood v. muscle). Alternatively, it may be selected so that changes in the ratio R are correlated to differences in S/N ratio, with larger Rs being correlated with signal and smaller Rs being correlated with speckle or electric noise. Optionally, different “selected frequency bands” may be used for near returns and for distant returns. For example, a wider frequency band may be used for signals that correspond to distant structures. In other words, the band selection can be a function of depth.

One suitable set of numeric values that results in a correlation between R and the material being imaged will now be discussed. Consider first the ultrasound return from a single scatter at a depth of r mm. The return from this scatter arrives after a time delay of t μs, given by

t=r/v=r/(0.77 mm/μs)=1.30 r μs,

where the scaling factor of 0.77 mm/μs represents a round trip from the transducer to the scatterer and back (assuming the velocity of sound in tissue is to be 1.54 mm/μs).

The effects of scatterer periodicity upon the spectrum of the demodulated ultrasound return may be calculated in the case of separations large enough so that the ultrasound returns do not overlap (i.e., separations Δr larger than Δr0=0.77 mm/μs×Δt). For example, in the case of an ideal one cycle pulse, a 5 MHz center frequency, and a ideal wide-bandwidth transducer,

Δt=1/fc=1/(5 MHz)=0.200 μs,

and thus

Δr0=0.77 mm/μs×0.200 μs=0.154 mm.

The internal structure of cardiac muscle displays variations on this and larger spatial scales. In contrast, scattering from blood is characterized by full-developed speckle, including variations on all, and especially much smaller spatial scales. As a result, low frequencies are indicative of muscle, and high frequencies are indicative of blood. This suggests defining the upper limit of a low frequency band to be less than about 4 MHz, corresponding to a minimal spatial scale ΔrMIN of

ΔrMIN=0.77 mm/μs×1/(4 MHz)=0.77 mm/μs×250 μs=0.193 mm.

The inventors have performed tissue experiments that used a signal digitized at 50 MHz (corresponding to sampling interval of 0.02 μs), and computed the FFT in a 64 point window (corresponding to 64×0.02 μs=1.28 μs, or 0.986 mm). With that size window, the inventors selected a low frequency band that included Fourier frequencies of between 2 and 5 cycles per window (inclusive), which corresponds to frequencies between 2/1.28 MHz=1.56 MHz and 5/1.28 MHz=3.91 MHz.
Using the formula for R set forth above (R=EBAND/ETOTAL) for this low frequency band, the ratio of Fourier power in the low frequency band to the total Fourier power is computed for each pixel. The end result of step 2 in FIG. 14 is a value of R for each pixel.
The inventors have found that, for the parameter values used in this example, R-values of around 0.45 are significantly correlated to the presence of muscle tissue at the pixel of interest, and R-values of around 0.20 are significantly correlated to blood or regions dominated by electronic noise. The remaining part of the algorithm uses this information to improve the image by increasing the intensity of the portions of the image that correspond to muscle and decreasing the intensity of the portions of the image that correspond to blood. Since blood is less reflective than muscle, this difference enhances the contrast between blood and muscle.
The inventors have determined that cardiac ultrasound images are dramatically improved when the intensity of the areas with R-values corresponding to muscle is increased to about 120% of its original value, and when the intensity of the areas with R-values corresponding to blood is decreased to between about 20% and 50% of its original value. Thus, in step 3 of FIG. 14, a gain factor of about 1.2 is assigned to those portions of the image with R values of about 0.45, and a gain factor of between about 0.2 and 0.5 is assigned to those portions of the image with R values of about 0.20. This gain factor is referred to herein and a “feature gain factor” or FGF because the gain is feature dependant.
While most pixels in most images will have R-values that permit the pixel to be classified as being either muscle or blood, in some cases the classification is less clear. For example, pixels that straddle a boundary between muscle and blood have less predictable R values. In addition, although the R-values from blood may average out to 0.20, any given pixel of blood may vary widely from that R-value due to random statistical variations. Accordingly, a monotonic, preferably smooth function may be used to map R to FGF in some embodiments. FIG. 15 is an example of a suitable function for this purpose. Optionally, additional restrictions may be built into the mapping function, based on other tissue characteristics.
Finally, in step 4 of FIG. 14, the results of the intensity algorithm and the frequency algorithm are combined by multiplying the intensity value for each pixel (obtained from the intensity algorithm) by the FGF value for that pixel (obtained from the frequency algorithm). The result is an enhanced image in which the pixels that are probably muscle have been brightened while the pixels that are probably blood have been dimmed. This enhanced image is then displayed using conventional hardware and software techniques (including, for example, using interpolation to convert the polar coordinates to rectangular coordinates).
The actual choice of the Fourier frequency bands, R-values and corresponding FGF values depends upon a variety of factors including but not limited to transducer center frequency, sampling rate, window size and any optional windowing techniques used in signal processing, transducer bandwidth, the width of interrogating pulse, etc. In one embodiment, for example, a transducer center frequency of 7.5 MHz is used, the scan line is digitized at about four times the center frequency (i.e., about 30 MHz), and the distance between the samples is about 0.026 mm.
In alternative embodiments, other normalized (i.e., non-amplitude-dependent measures) may be used instead of dividing EBAND by ETOTAL. For example, the ratio of power in a first frequency band to the power in a second frequency band may be used to compute R, as explained in the '215 patent (e.g., by dividing EBAND1 by EBAND2). In alternative embodiments, two or more Fourier analyses may be performed for each pixel, using a corresponding number of lines of samples, where the center of each line is contained within the pixel. For example, a two line per pixel arrangement in which a first ID Fourier analyses is implemented along a line of samples in the radial direction, and a second ID Fourier analyses is implemented along a second line of samples in the tangential direction. The results from those two lines of samples are then merged (e.g., by averaging). In still other embodiments, a 2D Fourier algorithm may be used instead of the ID algorithms described above.
Ordinarily, the above-described operations are performed on the uncompressed image data. Under certain circumstances, however, it may be possible to perform corresponding operations directly on a compressed version of the image data.
Once the enhanced images have been generated, they may be displayed using conventional hardware. The images may be continuously updated and displayed for the entire time that the probe is in position, so that the physician can visualize the patient's heart in real time. In alternative embodiments, images may be acquired and optionally stored periodically (e.g., by capturing one or more complete heartbeats every two minutes). Optionally, the ability to compare a prior heartbeat to the current heartbeat may be provided by, for example, playing back a stored video clip (or “loop”) of an old heartbeat in one window, and displaying the current image in a second window.
In contrast to conventional extended duration TEE using a transducer with a 10-15 mm azimuthal aperture, which is ordinarily done only under general anesthesia in the closely monitored environment of an room, the smaller diameter of the preferred embodiments described herein permits the preferred embodiments to be used without general anesthesia, and in less closely monitored environments. Optionally, the preferred embodiments may be used with sedation or local anesthesia in place of the general anesthesia that was used with conventional extended duration TEE. It may even be possible to forgo the use of sedation or anesthesia altogether. In such cases, the patient may optionally be medicated with an analgesic.
Optionally, regions of high relevance as detected by the feature gain factor may be highlighted, typically using colorization, while preserving the intensity of the gray-scale image, as explained in the '215 patent. Additional techniques for image enhancing can be found in Application Ser. No. 10/633,949, filed Aug. 4, 2003, and entitled “Method and Apparatus for Ultrasonic Imaging,” which is incorporated herein by reference.
The preferred embodiments described above advantageously permit non-invasive, intermediate and long-term monitoring of cardiac function using a small transducer that fits into a housing approximately 5 mm in diameter, thereby reducing or eliminating the need for anesthesia. The preferred embodiments described above combine a plurality of techniques to produce images that are comparable to or better than images that were conventionally obtained by much larger transducers. The images produced by the preferred embodiments described above are repeatably and reliably usable for monitoring heart function, with adequate penetration depth to see the far wall of the left ventricle (10-12 cm) and adequate resolution to determine LV size and function from an image of the endocardial wall in real time, despite the use of a smaller transducer. Thus, in contrast to prior art systems which provide a depth of penetration that is less than 15 times the azimuthal aperture of the transducer (e.g., obtaining 10 cm penetration using a 10 mm transducer) the preferred embodiments can provide penetration that is greater than 15 times the azimuthal aperture of the transducer, or even greater than 20 times the azimuthal aperture of the transducer (e.g., obtaining 10 cm penetration using a 4.75 mm transducer).
The preferred embodiments described above use a probe that is much narrower than conventional TEE probes, and may be used to monitor heart function over an extended period of time and to obtain an understanding of the patients' hemodynamic status. Such information may be useful in choosing treatments and improving outcome in many situations (including but not limited to critical medical problems such as hypotension, pulmonary edema and heart failure).
The above-described embodiments permit direct visualization of cardiac function, which permits evaluation of a patient's hemodynamic status including intravascular volume (normal, low or high), cardiac contractility (how well the left ventricle pumps), cardiac ischemia (inadequacy of blood flow to the heart muscle) and cardiac tamponade (fluid in the pericardial sac limiting heart function). For example, information about intravascular volume status can be derived from directly visualizing the size of the left ventricle and monitoring changes in size with treatments over time. Information about contractility can be obtained by directly visualizing the contraction (pumping) of the left ventricle, either using qualitative visual estimates or quantitatively. Information about ischemia is available during direct visualization of the left ventricle since ischemia results in abnormal motion of the walls of the left ventricle (wall motion abnormality). Information about possible cardiac tamponade or pericardial effusion (fluid in the heart sac) is available when using ultrasound to directly visualize the heart.
The narrowness of the probe may enable the above-described embodiments to provide this information for longer periods of time, outside the operating room, and/or without anesthesia. The above-described embodiments also lend themselves to use in settings where interventional cardiac procedures are performed such as the cardiac catheterization and electrophysiology laboratories, both for monitoring the effects of physicians' interventions on cardiac and hemodynamic function and for guiding the placement of devices. For example, they may be used to help the physician correctly place the pacing leads to achieve the desired result. The above-described embodiments may also be used in non-cardiac applications in which a narrower probe is needed or beneficial.
The above-described embodiments are not limited to ultrasound imaging modes, and may be used in alternative ultrasound modes (e.g., pulsed wave Doppler, continuous wave Doppler, and color flow imaging Doppler modes). These alternative modes may be performed using the same transducer as the above-described imaging modes and may yield information which can be combined with images, optionally in real-time. For example, color flow Doppler information may be obtained during imaging of the mitral valve (between the left atrium and left ventricle) while maintaining transducer position in the mid to lower esophagus. Such an application would permit evaluation of leakage of the mitral valve (mitral regurgitation or insufficiency).
If desired, the preferred embodiments described above may be scaled down for neonatal or pediatric use. In such cases, a transducer that is between about 2.5 and 4 mm in the azimuthal direction is preferable, with the elevation dimension scaled down proportionally. Because less depth of penetration is required for neonatal and pediatric patients, the operating frequency may be increased. This makes γsmaller, which permits the use of a smaller transducer element spacing (pitch), and a correspondingly larger number of elements per mm in the transducer. When such a transducer is combined with the above-described techniques, the performance should meet or surpass the performance of conventional 7.5 mm TEE probes for neonatal and pediatric uses.
The embodiments described herein may also be used in non-cardiac applications. For example, the probe could be inserted into the esophagus to monitor the esophagus itself, lymph nodes, lungs, the aorta, or other anatomy of the patient. Alternatively, the probe could be inserted into another orifice (or even an incision) to monitor other portions of a patient's anatomy.
If desired, the center frequency may be lowered (e.g., down to about 4.5 MHz) to provide additional depth of penetration when needed (e.g., for very large patients). Although this will also reduce the resolution, the result may be acceptable when very large structures are being imaged. Alternatively, the transducer size and housing diameter may be scaled up in size (e.g., to about 7 mm) if the reduced resolution results in unusable images.
Numerous alternative and optional features may be substituted and added to the above-described embodiment. One optional feature is digital beamforming using significant oversampling. For example, if the transducer is operated at 7 MHz, and the return is digitized at 30×frequency, 30×7 MHz=210 MHz digitization would be required. That data could then be downsampled by a factor of five to reduce the number of data points to a 42 MHz sample. Such downsampling would reduce the noise floor due to front-end noise by a factor of √5, (i.e., over 2 bits in power). Similarly, downsampling by a factor of 7 would reduce the noise floor by a factor of √7.
FIG. 16A depicts the front face of an alternative 2D transducer 500, which includes a 2D array of active elements 510. The concepts described herein can also be implemented using this type of transducer by making appropriate adjustments that will be apparent to persons skilled in the relevant arts.
FIG. 16B depicts the front face of another alternative 2D transducer design that is referred to as a “sparse 2D transducer.” The sparse 2D transducer 600 has a column 610 of “transmit” elements 611, used for transmitting the ultrasound, and a row 620 of receive elements 621 used for receiving the ultrasound signal. As shown, there is one element 630 common to both the column 610 of transmit elements and the row 620 of receive elements. This common element 630 may be used for transmission, reception, or both. This transducer design reduces electronic noise by using separate transmit and receive elements, which eliminates the need for electronic transmit/receive switches at the elements. The concepts described herein can also be implemented using this type of transducer by making appropriate adjustments that will be apparent to persons skilled in the relevant arts.
Note that for one-dimensional (1D) phased array transducers, focus in the azimuth direction is typically implemented by controlling the timing of the electrical pulses that are applied to each individual element of the transducer during the transmit process and controlling the timing with which electrical signals from each of those elements are combined during the receive process. This process is known as beamforming, and is well known to persons skilled in the relevant arts. But with a 1D transducer, beamforming does not help with focusing in the elevation direction.
As explained above, one way to improve the focus (and resolution) in the elevation direction is to use a transducer with an increased aspect ratio. This provides an improved depth of penetration and an improved ability to discriminate key features further out in the image, which is particularly important in the context of finding the boundary between heart wall and cavity in cardiac ultrasonic imaging. A number of alternative approaches for improving focus in elevation are described below.
One way to obtain improved focus in the elevation direction is to use a two-dimensional (2D) transducer 500 (as shown in FIG. 16A), and control the phasing of the signals to each of the individual elements 510 to provide focus in both the elevation and azimuth directions. Note that while FIG. 16A schematically depicts a 7×7 array of elements, a more preferable size for obtaining usable images would between 24×24 and 48×48 for square arrays, or between 16×32 and 32×64 for rectangular arrays. Unfortunately, the hardware for interfacing with such a transducer is much more complicated than for 1D transducers, and the additional wiring that is required to get the signals to and from the large number of transducer elements can dramatically increase the diameter of the probe to the point where it can no longer be used in certain anatomical locations (e.g., the esophagus).
FIG. 17 depicts another alternative transducer that improves focus in elevation, with respect to conventional transducers. This transducer 10a is similar is most respect to the transducer 10′ depicted above in connection with FIG. 8B, including the overall dimensions. However, instead of having a single row of elements L1-LN, the transducer 10a of this embodiment has three rows of elements A1-AN, B1-BN, and C1-CN, all affixed to a backing 12a. 
The wiring of the transducer 10a (not shown) may be configured so that the system that interfaces with the transducer 10a has access to each element A1-AN, B1-BN, and C1-CN individually. This arrangement is referred to herein as a 1.5D transducer. By providing individual access to each element to the transducer 10a, a coarse version of beam forming can be used to improve the focus in the elevation direction, e.g. by delaying the transmit pulse on the middle row of element B1-BN with respect to the transmit pulse on the top and bottom rows of elements so that the signals of all three rows of elements arrive simultaneously at the focal point (not shown). Although focus is improved, this arrangement has a number of drawbacks with respect to the 1D transducer 10′ shown in FIG. 8B: (a) the hardware for interfacing with the transducer 10a is more complicated than the corresponding hardware for interfacing with the transducer 10′; (b) three times as many wires, transmit amplifiers, receive amplifiers, and digitizers are needed to get the signals to and from the larger number of transducer elements; and (c) the driving voltage applied to the signal wire connected to each element must be increased to compensate for the smaller capacitance of the smaller elements. Note, however, that the magnitude of these drawbacks is not as severe as with the 2D transducer 500 (shown in FIG. 16A), so the 1.5D transducer may still be usable in situations where the full 2D transducer 500 is not.
An alternative wiring configuration may be used to wire up the transducer 10a that avoids the aforementioned disadvantages. In this configuration, all of the elements in any given column are wired together in parallel. In other words, in any given column i (for i equals 1 through N), element Ai, Bi, and Ci are all wired in parallel. When this wiring configuration is used, only N+1 wires are needed to drive the transducer: N individual signals plus one common return. Thus, each column only requires a single signal wire, a single transmit amplifier, a single receive amplifier, and a single digitizer. In addition, because all the elements in any given column are wired together in parallel, the resulting capacitance (looking in from any given signal wire) is the sum of the capacitance of each individual element in that column, which means that a lower driving voltage can be used. When this wiring configuration is used, the result is a transducer 10a that behaves in all relevant respects like the transducer 10′ discussed above in connection with FIG. 8B. Of course, by wiring all the elements in each column together in parallel, the ability to use beamforming to achieve focus in the elevation direction is lost. Note that while FIG. 17 depicts three rows of elements A, B, and C, the number of rows may be varied (e.g., 5 rows), but should preferably be relatively small. In addition, while FIG. 17 schematically depicts only 8 columns of elements, it is preferably to use a larger number of elements (e.g., about 32-40).
Obtaining good image quality at far distances is usually more difficult than at close distances because the strength of the ultrasound return decreases with increasing distance (depth-dependent attenuation), and because the beam width (e.g., expressed in mm or any other linear measure) increases with increasing depth. This makes improvements in image quality more beneficial at greater depths. The inventors have recognized that image quality can be improved by optimizing the focus of the transducer to distant portions of the image at which one would expect relevant structures to appear. For example, when imaging the TGSAV, improved images can be obtained by optimizing the focus of the transducer at a distance where the far wall of the left ventricle is expected to be. Since the far wall of the LV will usually be located between about 75 and 105 mm from the transducer in adults, optimizing the focus at about 85 mm works well for capturing images of TGSAV. This design point should provide improved elevation focusing in the range 60 mm to 120 mm, and especially in the range 75 mm to 105 mm. Meanwhile, at the near wall of the LV, the signal will usually be so strong that inexact focus can be tolerated.
In embodiments that employ a 2D or 1.5D transducer, the focus can be set to 85 mm in front of the transducer's face using beamforming techniques. However, it is also possible to optimize the focus to that depth (or any other desired depth) using a specially configured transducer that avoids most of the drawbacks associated with 2D and 1.5D transducers.
One approach for optimizing focus is to position an acoustic lens in front of the transducer 10 or 10′ (shown in FIGS. 7B and 8B, respectively). Acoustic lenses can also be used together with the transducer 10a shown in FIG. 17 when it is wired up with the elements in each column connected in parallel.
Another approach for optimizing focus is to configure the geometry of the front face of the transducer to provide the desired focusing. FIG. 18A shows an isometric view of such a transducer 10b with a curved front face. The illustrated transducer 10b includes a plurality of elements J1-JN arranged in a single row. All of these elements are connected to a backing 12b. Note that the X and Y axis in FIG. 18A are oriented differently in this view, so as to better show the curvature of the front face of the transducer 10b, and while only five elements J1-JN are depicted, it is preferable to use a larger number of elements (e.g. 32-40).
FIG. 18B is a side view of the first element J1 of the FIG. 18A embodiment. Although the remaining element J2-JN cannot be seen in FIG. 18B because they are directly behind element J1, the curvature of those elements is identical to the curvature of element J1. The front face of element J1 is shaped to follow a curve 16 that focuses the ultrasound curves emitted by the transducer. For example, focus may be set to a focal point 18 by using a curve in which all points on the curve are equidistant from a focal point 18 (i.e., a segment of a circle). Then, transmitted acoustic signals that travel from the front face of the element will all arrive at the focal point 18 at the same time, and return reflections from the focal point will also reach the front face of the element J1 simultaneously.
A focal point similar to the focal point 18 exists for each of the remaining elements J2-JN. When all the focal points J1-JN are viewed together, the locus of points forms a rod shaped focal region located at a particular radial distance in front of the transducer (with the rod's axis oriented so that it extends into and out of the page in FIG. 18B, i.e., parallel to the front face of the transducer). Note that deviations from an ideal rod shape and a perfectly parallel orientation may occur as a result of the elements not all being exactly the same size or not being perfectly aligned. Note also that the curvature 16 is exaggerated in all the figures. Note also that this portion of the discussion deals with focus in the elevation direction. Focus in the azimuthal elevation direction is preferably implemented dynamically using conventional beam forming techniques, in a manner that will be apparent to person skilled in the relevant arts.
Making the transducer taller in the elevation direction (i.e., maintaining a larger aspect ratio) is also desirable in this embodiment, and two exemplary sets of design parameters for the transducer 10b are set forth below in Table 5:









TABLE 5





Feature
First Example
Second Example







Size in the transverse (azimuthal)
about 4-5 mm
about 4-5 mm


direction




Number of elements
about 32-40
about 32-40


Size in the elevation direction
about 4-5 mm
about 8-10 mm


Front face aspect ratio
about 1:1
about 2:1


(elevation:transverse)




Operating frequency
about 6-7.2 MHz
about 6-7.2 MHz


Radius of curvature of curve 16
about 85 mm
about 75-105 mm









As explained above, a good focal distance for a transducer that is designed for imaging the TGSAV of an adult heart is about 85 millimeters. Accordingly, the curvature of the front face of the transducer 18B should preferably be cylindrical with a radius of 85 millimeters to optimize the transducer for that application. The improvement in performance when the front face of the transducer is cylindrical (as compared to a flat-faced 1D transducer) can be calculated as follows:
When a 1D flat-faced transducer with a 10 mm height (in elevation), configured as shown in either FIG. 8 or 17 is operated at 6.2 MHz, and positioned with its front face located 85 mm from the target, the phasing errors (i.e., the difference in distance from points on the front face from the nominal 85 mm target) are about 1⁄2 a wavelength (because the distance from the center of the transducer to the target is 85 mm and the distance from the edge of the transducer to the target is ν(852+52)=85.15 mm. At a speed of 1500 m/s this 0.15 mm difference corresponds to about 1⁄2λ).
For the curved-faced transducer depicted in FIGS. 18A and 18B, this 1⁄2λ phasing error is completely eliminated, which improves the amplitude of the ultrasound signal at the target focal point 18 by a factor of about 1.9, which is equivalent to about +51⁄2 dB. A similar gain is obtained on the receive path, providing a total round-trip (transmit and receive) improvement of about 11 dB at 6.2 MHz. Since the round trip loss in ultrasound systems is about 1 dB/(cm MHz), the loss for ultrasound systems operating at 6.2 MHz is about 6.2 dB/cm. The 11 dB improvement therefore corresponds to an increased penetration of about 1.8 cm (as compared to the flat-faced 1D transducer with a 10 mm elevation aperture).
FIG. 19 is a side view of another transducer embodiment in which the front face is shaped to match a curve 16 that focuses at focal point 18. However, this embodiment uses a plurality of rectangular transducer elements stacked on top of each other in the elevation direction. (instead of the single curved transducer element in each column as described above in connection with FIGS. 18A and 18B). The first column of elements contains a top element G1, a middle element H1, and a lower element H1, all wired together in parallel. Spacers 19 are located between the top element G1 and the middle element H1, and between the middle element H1 and the bottom element I1. These spacers 19 may be integral with the elements G1, H1, and I1, in which case the spacers 19 would merely represent regions of the a single piece of PZT (or other material of which ultrasound transducers are made). Alternatively, the spacers 19 may be made of a different material (e.g., epoxy) and each component may be formed from a separate piece of PZT. Although they cannot be seen in the side view depicted in FIG. 19, N additional columns of similar construction are stacked directly behind the first column, each column containing three elements that are wired together in parallel: Gi, Hi, and Ii (for each column i, where i varies from 1 to N). The transducer then consists of a plurality of composite elements that are stacked in the azimuth direction, with a front face that closely approximates an ideal cylindrical surface. The design parameters set forth above in Table 5 are suitable for this embodiment as well.
Wiring all three elements in each column together results in fewer wires, fewer active components, reduced complexity and increased capacitance (which means that a lower driving voltage can be used). Thus, when this wiring configuration is used, the transducer behaves from an electrical perspective respects like the transducer 10′ discussed above in connection with FIG. 8B, but provides improved focusing characteristics in elevation for the following reason: Since all three elements in each column are wired in parallel, the electrical excitation pulse arrives at all three elements at the same time, which causes the acoustic wave to leave the front face of all three elements at the same time. And since all three elements and are located on a curve 16 that is equidistant from the focal point 18 and are canted appropriately to face towards the focal point 18, the acoustic wave from each of the three elements in any given column arrives at the focal point at the same time. Furthermore, if an acoustically reflective object is located at the focal point 18, the acoustic energy that is reflected from the object will reach the front face of all three elements at the same time, which produces a sharper receive pulse that further improves the image. As in the FIG. 18B embodiment, the focal points of all the elements combine to form a rod-shaped focal region. Note that while this embodiment is described above with three elements (Gi, Hi, and Ii) in each column, different numbers of elements may be used instead (e.g., 5 elements per column, with all 5 elements wired in parallel).
For this embodiment, the phasing error is not completely eliminated, but is nevertheless drastically reduced. For example, using center elements Hi that measure 3 mm in elevation and top/bottom elements Gi, Ii, that measure 3.5 mm and are canted at 1 wavelength (248 μm) per mm in elevation (a slope selected to minimize maximum phasing errors), the longest path to the focal point 18 would be from the edge of an element, which is located ν(852+1.752)=85.018 mm away. This 0.018 mm difference corresponds to a worst-case phasing error of about 0.05λ, which yields an improvement over the flat-faced transducer that is almost as good as the improvement provided by the cylindrical-faced transducer described above in connection with FIGS. 18A and 18B.
FIGS. 20A and 20B are, respectively, side and isometric views of another transducer 12c in which the front face is shaped to match a curve 16 that focuses at focal point 18. This embodiment is similar to the transducer discussed above in connection with FIG. 19 in that each element i is made of a plurality of subelements Di, Ei, and Fi, with the elements in each column all wired together in parallel (for each column i, where i varies from 1 to N). However, instead of canting the subelements in the top and bottom rows toward a focal region, each of the subelements Di, Ei, and Fi face in the same direction (i.e., directly forward), preferably aligned so that the a front center of each face is positioned on a cylindrical curve 16. The design parameters set forth above in Table 5 are suitable for this embodiment as well.
Like the FIG. 19 embodiment, the transducer 12c has fewer wires, fewer active components, reduced complexity and increased capacitance, and behaves from an electrical perspective like the transducer 10′ discussed above in connection with FIG. 8B. And like the FIG. 19 embodiment, the transducer 12c provides improved focusing characteristics in the elevation direction. This occurs because all three elements in each column are wired in parallel, so the electrical excitation pulse arrives at all three elements at the same time, and the acoustic wave leaves the front face of all three elements at the same time. Since the center of each of the three elements is preferably located on a curve 16 that is equidistant from the focal point 18, the acoustic wave from the center of each element in any given column will arrive at the focal point at the same time, and acoustic reflections objects located at the focal point will return at the same time. As in the FIG. 18B embodiment, the focal points of all the elements combine to form a rod-shaped focal region. Note that while 3 elements per column are depicted, this embodiment may also employ a different number of elements per column (e.g., 5 elements per column, with all 5 elements wired in parallel).
The stepped-element transducer depicted in FIGS. 20A and 20B provides a dramatic improvement over a flat-faced transducer, but the results are not quite as good as the cylindrical-faced transducer depicted in FIG. 18 or the canted transducer depicted in FIG. 19. For example, if the center elements Ei, in FIG. 20 measures 5 mm in elevation and the top/bottom elements Di, Fi measure 2.5 mm and are offset forward by 1.9 wavelengths (472 μm), the resulting maximum phasing error would be about 1⁄4λ. This should improve the amplitude of the ultrasound signal at the target focal point 18 by a factor of about 1.6, which is equivalent to about +41⁄2dB in each direction, for a total of about 9 dB for the round-trip. This 9 dB improvement corresponds to an increased penetration of about 1.4 cm (as compared to a flat-faced 1D transducer with a 10 mm elevation aperture).
Note that for a transducer whose primary intended purpose is for imaging the TGSAV in adults, a design point of about 85 mm for the depth of field is preferable. As persons skilled in the relevant arts will appreciate, that design point can be scaled up or down based on the size of the patient that is being imaged. For example, a depth of focus of about 42 mm would be suitable for use with the 2.5 mm diameter neonatal TEE probe discussed above, and a depth of focus of about 65 mm would be suitable for the 4 mm diameter pediatric TEE probe. For cardiac views other than the TGSAV, or for imaging other anatomical (or non-anatomical) structures, appropriate changes to the geometry may be made to obtain any desired focal distance as will be appreciated by persons skilled in the relevant arts.
Note that while the examples discussed above in connection with FIGS. 18-20 are phased array transducers, similar geometries may be used with other types of ultrasound transducers (not shown) such as linear array transducers or curvilinear array transducers. With those transducers, a coarse type of azimuthal aiming is provided by arranging the elements into groups, and then exciting all the elements in a given group together. In one example, the center elements of a linear array transducers could be excited for near-field targets, and all the elements could be excited for far-field targets. In another example, the top, center, and bottom thirds of a curvilinear array may be excited separately to provide coarse aiming in the rising, straight, and falling directions, respectively. Aiming in the elevation direction is provided by dividing each element into subelements (e.g., 3 per element) and either canting the subelements towards a target region, and/or offsetting the elements so that they are equidistant from the target region, as illustrated above in FIGS. 19 and 20.
Alternative embodiments of the invention may use fewer techniques and/or implement those techniques to a lesser extent, and still maintain the ability to produce an acceptable image. For example, depending on the other components in the system, it may be possible to obtain an acceptable image using a 75° sector width, or even using a 90° sector width. It may also be possible to obtain an acceptable image using a transducer with an elevation:transverse aspect ratio of about 2:3 in place of the preferred 1:1 or 2:1 aspect ratios. Another alternative would be to use some or all of the above-described techniques with a transducer that is slightly larger than the preferred embodiments described above, yet still smaller than conventional 10 mm TEE transducer. Numerous other modifications to the above-described embodiments will be apparent to those skilled in the art, and are also included within the purview of the invention.

## Claims

1. A phased array ultrasound transducer comprising:
a plurality of independently excitable elements that are arranged in a row in the azimuthal direction, configured so that azimuthal aiming of an outgoing ultrasound beam is controlled by timing the excitation of the elements, wherein the height of the elements in the elevation direction is at least as large as the width of the row of elements in the azimuthal direction,
wherein each of the elements comprises at least three subelements that are stacked in the elevation direction, with all the subelements of any given element having signal lines that are hard-wired together in parallel, and
wherein all the subelements of any given element are positioned at about the same distance from a substantially rod-shaped real focal region located in front of the transducer.

2. The phased array ultrasound transducer of claim 1, wherein the subelements are canted appropriately so as to face towards the focal region.

3. The phased array ultrasound transducer of claim 1, wherein all the subelements face straight forward.

4. The phased array ultrasound transducer of claim 1, wherein the focal region is between about 60 and about 120 mm from the front of the transducer.

5. The phased array ultrasound transducer of claim 1, wherein the focal region is between about 75 and about 105 mm from the front of the transducer.

6. The phased array ultrasound transducer of claim 1, wherein the focal region is about 85 mm from the front of the transducer.

7. The phased array ultrasound transducer of claim 1, wherein the height of the transducer in the elevation direction is at least twice as large as the width of the transducer in the azimuthal direction.

8. The phased array ultrasound transducer of claim 1, wherein
the plurality of independently excitable elements that are arranged in a row in the azimuthal direction includes at least 20 independently excitable elements, and
the particular radial distance is between about 75 and about 105 mm.

9. A phased array ultrasound transducer comprising:
a plurality of independently excitable elements that are arranged in a row in the azimuthal direction, configured so that azimuthal aiming of an outgoing ultrasound beam is controlled by timing the excitation of the elements, wherein the height of the elements in the elevation direction is at least as large as the width of the row of elements in the azimuthal direction
wherein each of the elements comprises at least three subelements that are stacked in the elevation direction, with all of the at least three subelements having signal lines that are hard-wired together in parallel, and wherein the elements are configured to focus the outgoing beam in the elevation direction at a real focus located in front of the transducer so as to improve the images obtained from at or about a particular radial distance in front of the transducer.

10. The phased array ultrasound transducer of claim 9, wherein all the subelements face directly forward.

11. The phased array ultrasound transducer of claim 9, wherein all the subelements face towards a target region.

12. The phased array ultrasound transducer of claim 9, wherein the particular radial distance is between about 60 and about 120 mm.

13. The phased array ultrasound transducer of claim 9, wherein the particular radial distance is between about 75 and about 105 mm.

14. The phased array ultrasound transducer of claim 9, wherein the particular radial distance is about 85 mm.

15. The phased array ultrasound transducer of claim 9, wherein the height of the transducer in the elevation direction is at least as large as the width of the transducer in the azimuthal direction.

16. The phased array ultrasound transducer of claim 9, wherein the height of the transducer in the elevation direction is at least twice as large as the width of the transducer in the azimuthal direction.

17. The phased array ultrasound transducer of claim 9, wherein
the plurality of independently excitable elements that are arranged in a row in the azimuthal direction includes at least 20 independently excitable elements,
the height of the transducer in the elevation direction is at least as large as the width of the transducer in the azimuthal direction, and
the particular radial distance is between about 75 and about 105 mm.

18. An ultrasound transducer comprising:
a plurality of elements that are arranged in a row in the azimuthal direction, configured so that azimuthal aiming of an outgoing ultrasound beam is accomplished by controlling the excitation of the elements, wherein the height of the elements in the elevation direction is at least as large as the width of the row of elements in the azimuthal direction
wherein each of the elements comprises at least three subelements that are stacked in the elevation direction, with all of the at least three subelements having signal lines that are hard-wired together in parallel, and wherein the elements are configured to focus the outgoing beam in the elevation direction at a real focus located in front of the transducer so as to improve the images obtained from at or about a particular radial distance in front of the transducer.

19. The ultrasound transducer of claim 18, wherein all the subelements face towards a target region.

20. The ultrasound transducer of claim 18, wherein all the subelements face directly forward.